US3587730A - Heat exchange system with porous boiling layer - Google Patents

Heat exchange system with porous boiling layer Download PDF

Info

Publication number
US3587730A
US3587730A US46291A US3587730DA US3587730A US 3587730 A US3587730 A US 3587730A US 46291 A US46291 A US 46291A US 3587730D A US3587730D A US 3587730DA US 3587730 A US3587730 A US 3587730A
Authority
US
United States
Prior art keywords
boiling
liquid
porous
heat
heat transfer
Prior art date
Legal status (The legal status is an assumption and is not a legal conclusion. Google has not performed a legal analysis and makes no representation as to the accuracy of the status listed.)
Expired - Lifetime
Application number
US46291A
Inventor
Robert M Milton
Current Assignee (The listed assignees may be inaccurate. Google has not performed a legal analysis and makes no representation or warranty as to the accuracy of the list.)
Union Carbide Corp
Original Assignee
Union Carbide Corp
Priority date (The priority date is an assumption and is not a legal conclusion. Google has not performed a legal analysis and makes no representation as to the accuracy of the date listed.)
Filing date
Publication date
Priority claimed from US366853A external-priority patent/US3384154A/en
Application filed by Union Carbide Corp filed Critical Union Carbide Corp
Application granted granted Critical
Publication of US3587730A publication Critical patent/US3587730A/en
Assigned to MORGAN GUARANTY TRUST COMPANY OF NEW YORK, AND MORGAN BANK ( DELAWARE ) AS COLLATERAL ( AGENTS ) SEE RECORD FOR THE REMAINING ASSIGNEES. reassignment MORGAN GUARANTY TRUST COMPANY OF NEW YORK, AND MORGAN BANK ( DELAWARE ) AS COLLATERAL ( AGENTS ) SEE RECORD FOR THE REMAINING ASSIGNEES. MORTGAGE (SEE DOCUMENT FOR DETAILS). Assignors: STP CORPORATION, A CORP. OF DE.,, UNION CARBIDE AGRICULTURAL PRODUCTS CO., INC., A CORP. OF PA.,, UNION CARBIDE CORPORATION, A CORP.,, UNION CARBIDE EUROPE S.A., A SWISS CORP.
Assigned to UNION CARBIDE CORPORATION, reassignment UNION CARBIDE CORPORATION, RELEASED BY SECURED PARTY (SEE DOCUMENT FOR DETAILS). Assignors: MORGAN BANK (DELAWARE) AS COLLATERAL AGENT
Anticipated expiration legal-status Critical
Expired - Lifetime legal-status Critical Current

Links

Images

Classifications

    • FMECHANICAL ENGINEERING; LIGHTING; HEATING; WEAPONS; BLASTING
    • F28HEAT EXCHANGE IN GENERAL
    • F28FDETAILS OF HEAT-EXCHANGE AND HEAT-TRANSFER APPARATUS, OF GENERAL APPLICATION
    • F28F13/00Arrangements for modifying heat-transfer, e.g. increasing, decreasing
    • F28F13/18Arrangements for modifying heat-transfer, e.g. increasing, decreasing by applying coatings, e.g. radiation-absorbing, radiation-reflecting; by surface treatment, e.g. polishing
    • F28F13/185Heat-exchange surfaces provided with microstructures or with porous coatings
    • F28F13/187Heat-exchange surfaces provided with microstructures or with porous coatings especially adapted for evaporator surfaces or condenser surfaces, e.g. with nucleation sites
    • FMECHANICAL ENGINEERING; LIGHTING; HEATING; WEAPONS; BLASTING
    • F25REFRIGERATION OR COOLING; COMBINED HEATING AND REFRIGERATION SYSTEMS; HEAT PUMP SYSTEMS; MANUFACTURE OR STORAGE OF ICE; LIQUEFACTION SOLIDIFICATION OF GASES
    • F25JLIQUEFACTION, SOLIDIFICATION OR SEPARATION OF GASES OR GASEOUS OR LIQUEFIED GASEOUS MIXTURES BY PRESSURE AND COLD TREATMENT OR BY BRINGING THEM INTO THE SUPERCRITICAL STATE
    • F25J5/00Arrangements of cold exchangers or cold accumulators in separation or liquefaction plants
    • F25J5/002Arrangements of cold exchangers or cold accumulators in separation or liquefaction plants for continuously recuperating cold, i.e. in a so-called recuperative heat exchanger
    • F25J5/005Arrangements of cold exchangers or cold accumulators in separation or liquefaction plants for continuously recuperating cold, i.e. in a so-called recuperative heat exchanger in a reboiler-condenser, e.g. within a column
    • FMECHANICAL ENGINEERING; LIGHTING; HEATING; WEAPONS; BLASTING
    • F25REFRIGERATION OR COOLING; COMBINED HEATING AND REFRIGERATION SYSTEMS; HEAT PUMP SYSTEMS; MANUFACTURE OR STORAGE OF ICE; LIQUEFACTION SOLIDIFICATION OF GASES
    • F25JLIQUEFACTION, SOLIDIFICATION OR SEPARATION OF GASES OR GASEOUS OR LIQUEFIED GASEOUS MIXTURES BY PRESSURE AND COLD TREATMENT OR BY BRINGING THEM INTO THE SUPERCRITICAL STATE
    • F25J2250/00Details related to the use of reboiler-condensers
    • F25J2250/02Bath type boiler-condenser using thermo-siphon effect, e.g. with natural or forced circulation or pool boiling, i.e. core-in-kettle heat exchanger
    • FMECHANICAL ENGINEERING; LIGHTING; HEATING; WEAPONS; BLASTING
    • F25REFRIGERATION OR COOLING; COMBINED HEATING AND REFRIGERATION SYSTEMS; HEAT PUMP SYSTEMS; MANUFACTURE OR STORAGE OF ICE; LIQUEFACTION SOLIDIFICATION OF GASES
    • F25JLIQUEFACTION, SOLIDIFICATION OR SEPARATION OF GASES OR GASEOUS OR LIQUEFIED GASEOUS MIXTURES BY PRESSURE AND COLD TREATMENT OR BY BRINGING THEM INTO THE SUPERCRITICAL STATE
    • F25J2250/00Details related to the use of reboiler-condensers
    • F25J2250/04Down-flowing type boiler-condenser, i.e. with evaporation of a falling liquid film
    • FMECHANICAL ENGINEERING; LIGHTING; HEATING; WEAPONS; BLASTING
    • F25REFRIGERATION OR COOLING; COMBINED HEATING AND REFRIGERATION SYSTEMS; HEAT PUMP SYSTEMS; MANUFACTURE OR STORAGE OF ICE; LIQUEFACTION SOLIDIFICATION OF GASES
    • F25JLIQUEFACTION, SOLIDIFICATION OR SEPARATION OF GASES OR GASEOUS OR LIQUEFIED GASEOUS MIXTURES BY PRESSURE AND COLD TREATMENT OR BY BRINGING THEM INTO THE SUPERCRITICAL STATE
    • F25J2290/00Other details not covered by groups F25J2200/00 - F25J2280/00
    • F25J2290/44Particular materials used, e.g. copper, steel or alloys thereof or surface treatments used, e.g. enhanced surface
    • FMECHANICAL ENGINEERING; LIGHTING; HEATING; WEAPONS; BLASTING
    • F28HEAT EXCHANGE IN GENERAL
    • F28DHEAT-EXCHANGE APPARATUS, NOT PROVIDED FOR IN ANOTHER SUBCLASS, IN WHICH THE HEAT-EXCHANGE MEDIA DO NOT COME INTO DIRECT CONTACT
    • F28D21/00Heat-exchange apparatus not covered by any of the groups F28D1/00 - F28D20/00
    • F28D2021/0019Other heat exchangers for particular applications; Heat exchange systems not otherwise provided for
    • F28D2021/0033Other heat exchangers for particular applications; Heat exchange systems not otherwise provided for for cryogenic applications
    • FMECHANICAL ENGINEERING; LIGHTING; HEATING; WEAPONS; BLASTING
    • F28HEAT EXCHANGE IN GENERAL
    • F28FDETAILS OF HEAT-EXCHANGE AND HEAT-TRANSFER APPARATUS, OF GENERAL APPLICATION
    • F28F2255/00Heat exchanger elements made of materials having special features or resulting from particular manufacturing processes
    • F28F2255/18Heat exchanger elements made of materials having special features or resulting from particular manufacturing processes sintered
    • YGENERAL TAGGING OF NEW TECHNOLOGICAL DEVELOPMENTS; GENERAL TAGGING OF CROSS-SECTIONAL TECHNOLOGIES SPANNING OVER SEVERAL SECTIONS OF THE IPC; TECHNICAL SUBJECTS COVERED BY FORMER USPC CROSS-REFERENCE ART COLLECTIONS [XRACs] AND DIGESTS
    • Y10TECHNICAL SUBJECTS COVERED BY FORMER USPC
    • Y10STECHNICAL SUBJECTS COVERED BY FORMER USPC CROSS-REFERENCE ART COLLECTIONS [XRACs] AND DIGESTS
    • Y10S159/00Concentrating evaporators
    • Y10S159/28Porous member
    • YGENERAL TAGGING OF NEW TECHNOLOGICAL DEVELOPMENTS; GENERAL TAGGING OF CROSS-SECTIONAL TECHNOLOGIES SPANNING OVER SEVERAL SECTIONS OF THE IPC; TECHNICAL SUBJECTS COVERED BY FORMER USPC CROSS-REFERENCE ART COLLECTIONS [XRACs] AND DIGESTS
    • Y10TECHNICAL SUBJECTS COVERED BY FORMER USPC
    • Y10STECHNICAL SUBJECTS COVERED BY FORMER USPC CROSS-REFERENCE ART COLLECTIONS [XRACs] AND DIGESTS
    • Y10S165/00Heat exchange
    • Y10S165/183Indirect-contact evaporator

Definitions

  • This invention relates to the art of improving heat transfer from heated surfaces to boiling liquids.
  • FIG. I is a curve which compares the properties of the porous boiling surface layers of this invention with the surfaces of the prior art.
  • FIG. 2 is a series of curves comparing the pool boiling performance of the porous boiling surface layers of this invention with the surfaces of the prior art.
  • FIGS. 3-4 are sectional views in elevation of an exemplary plate-and-fin type heat exchanger illustrating embodiments of the invention.
  • FIG. 5 is a sectional view in elevation of an exemplary condensing surface embodying the invention.
  • FIG. 6 is a view partly in elevation and partly in section of an exemplary boiling surface and condensing surface element in the form of a condenser-evaporator tube member embodying the invention.
  • FIG. 7 is a fragmentary enlarged view in section of a portion of the tube unit.
  • FIG. 8 is a view showing a preferred inclined arrangement of a condenser-evaporator tube according to the invention.
  • FIG. 9 is a fragmentary end view of a preferred arrangement of such tubes when mounted in groups.
  • FIG. 10 is a perspective view of an alternative construction of evaporator-condenser units embodying the invention.
  • a porous boiling surface layer having a multitude of small pores bonded on a thermally conductive wall of a heat exchange apparatus for transferring heat to a liquid.
  • the porous boiling surface layer is formed of thermally conductive particles integrally and. thermally bonded together to provide interconnected pores of capillary size within the porous boiling surface layer.
  • the pores are provided in great number per unit area with little nonporous material between them.
  • the porous boiling surface layer is characterized by pronounced capillarity which is described in detail subsequently.
  • Porous boiling surface layers of this invention have been found particularly advantageous in systems requiring elevated pressures to achieve a necessary temperature difference; for example in the reboiler-condenser tubes of a low temperature air separation plant wherein the more volatile normally lower temperature boiling nitrogen gas is condensed by boiling less volatile oxygen liquid, the nitrogen being sufficiently pressurized to raise its condensing temperature above the oxygen boiling temperature.
  • the necessary pressure differential between the fluids may be reduced and power costs minimized.
  • the preferred procedure for producing a satisfactory porous boiling surface layer comprises sintering, soldering, brazing, or otherwise thermally bonding a layer of fine particles to the base heat transfer surface to form interconnected pores therein having an equivalent pore radius less than about 6.0 mils.
  • the equivalent pore radius empirically defines a porous boiling surface layer having varied pore sizes and nonuniform pore configurations in terms of an average uniform pore dimension.
  • porous boiling surface layer of this invention An important function of the porous boiling surface layer of this invention is to increase the boiling heat transfer coefficient.
  • the effect of the increase in this coefficient can be utilized in several ways.
  • the total quantity of heat transferred Q may be increased, the area A may be decreased, the AT may be reduced, or various combinations of these benefits may be realized.
  • ebullators which are commonly suspended or immersed in the boiling liquid to reduce superheat and to bring the bulk liquid temperature more nearly in equilibrium with the liquids vapor pressure.
  • Ebullators are often nonmetallic materials such as pumice which contain relatively large random-size pores, only a few of which need be active.
  • the task of the ebullator is relatively easy and simple because the sensible heat represented by a few degrees superheat in the liquid is comparatively small and can be dissipated effectively by a modest degree of boiling.
  • the suspended ebullator material need not be thermally conductive since it does not transfer heat to the liquid.
  • the porous boiling surface layer of this invention is disposed on the hot wall of the boiling device between the hot wall and the liquid to be boiled and its material must be thermally conductive.
  • lts task is the more difficult one of transferring a very large quantity of heat with a greatly reduced heat flow resistance, i.e. with a reduced temperature difference between the warm wall and the liquid.
  • This temperature difference between the warm wall and the saturated liquid, which is a measure of the heat flow resistance, is the AT which appears in the standard heat transfer equation. lts reduction is achieved herein by the increased heat transfer coefficient ofthe porous boiling surface layer.
  • porous surface must meet special limitations on the equivalent pore radius as defined hereinafter.
  • T Temperature of liquid surrounding a bubble, "R.
  • TT is the minimum superheat required to sustain the boiling process.
  • the superheat necessary for bubble growth is reduced, i.e. TT is minimized, by increasing r, and hence an ebullator should be constructed with a porous surface having pores as large as possible which can still retain the entrapped gas or vapor needed to activate the nucleation cites.
  • Curve A plots r, vs. the superheat AT necessary to sustain bubble growth, i.e.
  • FIG. 1 shows that whereas ebullator coatings might reduce the required superheat AT (Curve A) to a very low value, the coincident filmAT is very high and exerts an overwhelming influence.
  • porous boiling surface layers of this invention are unique in that they effectively reduce the film AT and are therefore characterized by performance at the minimum'portion of the curve where the film AT begins to lose its dominant influence and where values ofr are below 6 mils.
  • the equivalent pore radius, r should be below about 4.5 mils.
  • Curves A and B of FIG. 1 represent the results obtained with fluorotrichloromethane as described above.
  • Other liquids will provide similar curves, which due to the individual pro-- perties of each liquid will be, in general, displaced along the abscissa.
  • a porous boiling surface layer constructed according to the present invention will have an equivalent pore radius of less than about 6.0 mils and preferably less than about 4.5 mils.
  • FIG. 2 shows in an even more striking manner the distinctive groupingof the porous boiling surfaces apart from conventional surfaces.
  • the surfaces tested correspond to those listed in Table I and the curves are numbered accordingly.
  • Prior art boiling surfaces have not approached the extremely high coefficients (heat flux per unit AT) which are obtained in this invention as exemplified by FIG. 2.
  • the equivalent pore radius of a porous boiling surface layer is most conveniently and accurately determined by vertically immersing one end of the porous boiling surface layer in a freely wetting liquid and measuring the capillary rise of the liquid along the surface of the porous boiling surface layer.
  • the equivalent pore radius, r is equal to 2cr/ph where: p is the density (in lbs. mass/cu. ft.) of the liquid in which an end of the porous boiling surface layer is vertically immersed: ois the surface tension (in lbs.
  • the advantage in choosing a freely wetting liquid to determine the equivalent pore radius is that the liquid phase contact angle (0), which the liquid surface makes with the materials of which the porous boiling surface layer is composed, will be very small and, therefore, will not effect the determination. If a freely wetting liquid is not chosen, the expression 2o'lph must be equated to r/cos 0 and the contact angle (6) will have to be accounted for in determining the value of the equivalent pore radius (r). Since the exact measurement of the contact angle is difficult and unnecessarily introduces risk of error, it is preferable to use a freely wetting liquid to determine the equivalent pore radius.
  • Liquids exhibiting a contact angle of less than 20 with the material of which the porous boiling surface layer is composed are defined as "freely wetting" for this purpose and may be used without having to account for the effect of the contact angle since cos 20 is 0.95 and the error resulting from neglecting the contact angle will be less than 5 percent.
  • suitable liquids which freely wet aluminum and copper surfaces are methanol, fluorotrichloromethane, dichlorotetrafluoroethane. acetone, ethyl chloride, liquid oxygen and liquid nitrogen.
  • the particular liquid chosen for determination of the equivalent pore radius should preferably be a good solvent for oil and grease so that the effect of the presence of these common surface contaminants will be minimized.
  • Pure water is not considered to be a freely wetting liquid inasmuch as its contact angle (0) with an aluminum surface, for example, is about 66.
  • the equivalent pore radius is independent of the properties of the material used to construct the porous boiling surface layer. It defines qualitatively the geometrical and dimensional characteristics of the porous boiling surface layer itself. The equivalent pore radius should not be employed to predict the quantitative performance of any particular porous boiling surface layer inasmuch as such performance will depend, inter alia, on the material of which the porous boiling surface layer is constructed and the liquid which is to be boiled.
  • Table I column 2 summarizes the values of the effective pore radius determined experimentally for a number of surfaces including prior art ebullators as well as porous boiling surface layers of the present invention in freely wetting liquidsspecifically methanol, fluorotrichloromethane, and dichlorotetrafluoroethane.
  • Column 3, of Table I shows the values of temperature differences required by the several surfaces to transfer 1,000 B.t.u./hr. sq. ft. while boiling fluorotrichloromethane. Since Q/A is held constant at l,000, the only variable in the heat transfer equations are AT and h, and these variables are inversely proportional. Consequently, a decrease in the required AT by a factor of will increase the heat transfer coefficient h by a factor of l0. Thus, column 3 of Table l provides a means of comparing the heat transfer capabilities ofthe various surfaces in a common fluid.
  • a porous boiling surface layer in operation provides a multitude of interconnecting partially liquid filled capillaries which act as nuclei for the growth of many bubbles of the boiling liquid lf the pores were not interconnected, their continued performance as nuclei for bubble growth would be critically dependent upon retaining entrapped air or vapor within the pores.
  • vapor formed in one pore can activate one or several adjacent pores, so that the process continues without interruption and without dependence upon air or vapor entrapment. At least some of the pores in the interconnected matrix are also believed to supply liquid to adjacent pores.
  • the above-described performance of a porous boiling surface layer is not merely the result of increasing the surface area by, for example, mechanically roughening the surface.
  • Table 11 indicates that by using a porous boiling surface of this invention, even a metal such as nickel exhibits boiling coefficients far greater than those obtained with conventional surfaces of highly conductive copper, despite the fact that the conductivity of nickel is only one-sixth that of copper.
  • the powder particles used in preparing the porous boiling surface are preferably either granular or spherical. Geometrical considerations suggest that granular or spherical particles are more effective than flakes in producing a large number of approximately uniform sized pores. Very thin flakes are less desirable since they are difficult to bond as discrete particles, and because their extremely large surface area complicates the task of cleaning the powder thoroughly
  • a comparison of items 1 and 4 (spherical) with items 2, 3 and 5 (granular) in Table I and FIG. 2 shows that both granular and spherical particles produce excellent surfaces. with spherical particles showing some advantage.
  • any metallic material is suitable for preparing the porous boiling surface, provided it has good thermal conductivity, is available as a fine powder, is bondable to itself and to the base metal, and is easily wetted by the liquid to be boiled.
  • the particle material should preferably have high thermal conductivity as stated previously.
  • nickel and copper porous boiling surface layer materials on copper base metal have been tested under identical conditions; the copperon-copper heat transfer coefficient being about three times as large as the nickel-on-copper combination which is to be ex pected because of the higher thermal conductivity of copper.
  • FIG. 2 where the performance of fine-mesh copper surfaces (curves 1 and 2) is better than fine-mesh aluminum surface (curve 3).
  • the conductivities of copper and aluminum are 224 and 117 B.t.u./hr. sq. ft. F./ft., respective ly. ln corrosive service, alloys, such as stainless steel, resistent to chemical attacks may be used.
  • the optimum thickness of the porous boiling surface is only slightly affected by the physical properties of the boiling liquid. This is indicated by tests wherein high boiling heat transfer coefficients are obtainable in stream-water service from a porous boiling surface having a thickness previously determined as optimum for oxygen service.
  • the thickness of the porous boiling surface layer may vary by at least a factor of 10 without severe detriment.
  • the thickness should be greater than the average particle diameter and preferably should be at least twice the average particle diameter. With fine particles such as 323 mesh, uniformity and complete continuity of the coating will usually govern the minimum thickness which is applied.
  • a practical minimum thickness is about 0.1 mm.
  • the maximum thickness which can be used without detriment is controlled only by the capillarity of the surface and by the ability of the surface to discharge the vapor produced in boiling. in operation, the surface should be capable of drawing the liquid all the way through the thickness to the base metal so that the surface is completely wetted, while at the same time discharging and disengaging the vapor from the pores.
  • Excellent results have been obtained with relatively thick surfaces; for example, the porous boiling surface layer of item 1 ofTable l and ofFlG. 2 is 0.25 mm. thick.
  • porous boiling surfaces can be formed of powder having very fine granular or spherical particles l50 microns in size. Such porous boiling surfaces have exhibited very high boiling heat transfer coefficients in tests with liquid oxygen and with water. However, other tests indicate that there is very little performance difference in boiling liquid oxygen between porous boiling surfaces produced from fine powder, e.g. screen analysis showing a major portion (98 percent) passing through 325 mesh (98 percent 44 microns), and coarse powder, e.g. 50-60 percent passing through 100 mesh (50- 60 percent 150 microns). If present in sufficient number, the smaller particles determine the pore dimensions since they will fill the voids between the large particles.
  • a suitable porous surface according to the invention may be produced by sintering l to 50 micron-size particles of a heat conductive metal such as copper to the hot wall supplying heat to the boiling liquid.
  • the particles are applied in such quantity to provide a porous layer thickness between about 0.l mm. and 1.0 mm.
  • the interstices or voids between the particles should be essentially free of solid material and should be interconnected within the depth of the layer.
  • the interconnected pores thus formed will be between about 1 micron and microns in size and there will be a great number per unit area of surface.
  • the equivalent radius of the pores of the porous boiling surface layer is the critical factor and that particle size alone is not necessarily determinative.
  • the particle size distribution within the range of sizes present in the sample will also influence the pore size. Particle shape will have an effect since spheres, for example, will stack more compactly than irregular shapes and will produce smaller voids.
  • the innumerable variations which these factors permit makes it impractical to bracket all suitable powders within a single specification. For this reason, the equivalent pore radius determined by routine testing on specimens of the finished porous boiling surface layer as described previously is technically a more accurate method of identification.
  • a temporary binder such as a plastic material to establish and maintain a uniform coating on the base metal surface, the binder being such that it decomposes and vaporizes during the heating and sintering process.
  • a temporary binder such as a plastic material to establish and maintain a uniform coating on the base metal surface, the binder being such that it decomposes and vaporizes during the heating and sintering process.
  • a plastic is an isobutylene polymer having a molecular weight of about 140,000 and known commercially as
  • the plastic binder is dissolved in an appropriate solvent such as kerosene or carbon tetrachloride and sufficient metal powder is added to give a uniform viscous slurry with a metalplastic weight ratio of about 92 to 1.
  • the base metal surface must be free of grease, oil and oxide coating to obtain proper bonding of the porous coating. Just before applying the slurry, the surface may be flushed with the plastic solution to facilitate wetting by the slurry, thereby
  • a number of methods may be used for applying a slurry coating to the base metal.
  • the object is to achieve a uniform coating, and the selection of the method will depend upon the geometry and orientation of the surface. Spraying and dipping are two procedures which have been used successfully.
  • the coating is air dried either during or after the application procedure.
  • the bulk of the solvent is thus removed by evaporation leaving a solid, self-supporting layer which is held in place by the binder.
  • the base metal and the coating are blanketed with a mildly reducing atmosphere and the temperature is raised for a sufficient time to sinter the particles together and to the base metal.
  • the circulating reducing gas removes the thin oxide film and also purges the decomposition products from the surface materials.
  • the coating is sintered at about F. below its melting point, or about 1,760 F.
  • Another successfully employed binder is a methyl cellulose polymer having a viscosity of 4,000 c.p.s. and known commercially as Methocel.
  • a preferred slurry comprises 32 grams of copper powder in l00 cc. of a 2 percent water solution of such polymer. After application of a coating of the slurry on the base metal, it is air dried at ordinary temperatures (below the boiling point of water), and then furnace dried at about 750 F. in an atmosphere of water saturated annealing gas. The coating is then sintered at appropriate sintering temperatures.
  • Still another plastic binder which is successfully used in polystyrene which has a molecular weight of about 90,000 and is soluble in toluene or xylene.
  • binders and slurries are used to facilitate distribution and to hold the powder temporarily in place until a permanent thermal bond can be achieved.
  • surface arrangement permits the powder may be applied and sintered in dry form; for example, the surface reported as item 1 in Table land FIG. 2 was prepared in this manner.
  • One arrangement consists of applying the porous boiling surface on the inner wall of heat exchanger tubes.
  • an excellent procedure is to preliminarily distribute the slurry within the length of the tube, and then place the tube in a machine capable of rotating the tube about its own axis at a rate sufficient to produce a smooth coating, about 200 r.p.m.
  • the coating is air dried during the spinning operation and is then furnace sintered under the conditions previously described.
  • Another application procedure lends itself particularly to flat, corrugated or outside-cylindrical surfaces.
  • a slurry of metal powder and plastic binder is fed from a hopper'onto the outer surface of a polished roll in a uniform layer.
  • the evaporation of the vehicle sets the plastic film and the latter is continuously stripped off the roll as a sheet of the plastic material containing the embedded metal powder.
  • the composite film is then placed in contact with the surface of a metal sheet which is conducted into the furnace wherein the plastic is vaporized and the metal powder sintered to the sheet.
  • FIG. 3 One preferred construction of a heat exchange apparatus employing a porous boiling surface layer is shown in FIG. 3.
  • This apparatus is a plate-type heat exchanger comprising a plurality of fluid passes defined by parallel, spaced parting sheets housed in a core section with appropriate headers and manifolds for the fluid streams.
  • thermally conductive metal walls in the form of parting sheets 1 and 2, which define the fluid pass 3 for the boiling liquid are'coated with a porous boiling surface layer 4, the fluid passes on either side offluid pass 3 being provided for the warm fluid supplying heat to vaporize the liquid within the pores of the porous boiling surface layer.
  • Protrusions 9 and from the parting sheets are in registry and abut with one another to form stays between the passage walls.
  • FIG. 4 shows another preferred construction for boiling condensing service using a flat plate type heat exchanger with corrugated fins in the passages.
  • the boiling passage is formed between parting sheets 1 and 2 and contains fin material 5 with corrugations widely spaced, e.g. 6 per inch. All exposed surfaces in the boiling passage are shown coated with porous boiling surface layer 4.
  • the condensing passage is formed between parting sheets 2 and 3 and contains fin material 6 with corrugations closely spaced, e.g. 25 per inch.
  • the closely spaced fins provide high surface area and distribute the condensate in a thinner layer of lower heat flow resistance. This increase h A with respect to h A, and brings these factors into balance.
  • FIG. 3 also shows such a condensing surface constructed in the form of very fine corrugations 6 which permit condensed liquid to be drawn by surface tension to the valleys 7 of the corrugations leaving the crests 8 stripped of all but a thin layer of liquid as shown in FIG. 5.
  • the utility of a condensing surface such as shown in FIG. 5 is not limited to plateand-fin type heat exchangers such as shown in FIG. 3.
  • such a surface may be applied to the exterior surfaces of tubes in shell-and-tube type heat exchangers where a porous boiling surface layer is bonded to the interior surface of the tubes.
  • a condensable vapor contacts the corrugated surface 6 and forms a condensate film thereon.
  • the film or more precisely the vapor liquid interface, acts as a membrane which is stretched elastically by surface tension over the crests of the corrugations. Therefore, the pressure in the liquid under the interface in the arc of each crest is greater than the pressure of the vapor above the interface. In the valleys 7, the curvature of the liquid-vapor interface is reversed and the tension therein produces the opposite efiect; the pressure in the liquid is less than the pressure of the vapor.
  • the condensate flows into the valley leaving a very thin film over the crest. Once in the valleys, the condensate flows parallel to the valleys (normal to the plane of FIG. 5) under the force of gravity to a suitable manifold means where it is withdrawn from the condensing surface.
  • the crests and valleys are too wide, the radius of curvature of the interfacial membrane will be large and the surface tension effect small. If the corrugations are too shallow, the valleys will have insufficient liquid-holding capacity and the crest area will flood. If the corrugations are too deep, the effectiveness of the interfacial membrane tension in the crest area will be reduced. Satisfactory dimensions must be designed with consideration of the condensing-liquid density, viscosity, surface tension, and the like. Usually, the valley 7 and crest 8 of the corrugations would have semicircular cross sections with radii between about 0.005 and 0.015 inches.
  • FIGS. 6 and 7 of the drawings show another embodiment of the present invention comprising a thermally conductive metal tube 10 which is provided on its internal boiling surface 11 with a porous boiling surface layer 12 formed of metal powder particles sintered to each other and to the inside surface of the tube 10.
  • the outer surface of the tube is preferably provided with fins or flanges 13 metallically bonded or molecularly integral with the tube 10 for most efficient heat conduction.
  • a plurality of such finned tubes is mounted between headers in areboilengopdenser portion of an apparatus for air separation by low-temperature rectification into its primary constituents oxygen and nitrogen wherein gaseous nitrogen at approximately 60-l00 p.s.i.
  • the ends of the tube unit may be constructed for mounting in openings, tube headers being preferably expanded to a larger diameter as shown at 14 and 15.
  • FIG. 8 for clearness of illustration, only one tube unit 10 is shown mounted between headers 16 and 17 which seal off lower and upper portions of a condenser casing 18, the tube ends 14 and 15 being secured gas-tightly in corresponding openings of the headers.
  • the casing ends are capped at 19 and 20 to form inlet and outlet chambers for liquid to be boiled, such as oxygen supplied through a conduit 21 and for collection of the resulting vapor which is led off by a conduit 22.
  • the vapor, such as cold nitrogen to be condensed is conducted to an upper part of the casing 18 through a connection 23, and the resulting condensate, liquid nitrogen, may be led off through a lower connection 24.
  • tubes 10 as are required are mounted between headers of suitable size.
  • FIGS. 5 and 7 Some geometric similarity may be noticed between FIGS. 5 and 7, but functionally they are quite different. As stated above condensate collects by surface tension in the very narrow valleys of FIG. 5 and runs off normal to the view of FIG. 5. In contrast, the fins of FIG. 7 are spaced wider apart so that condensate, tending to flow longitudinally of the tube, is instead diverted or stripped away from the tube and flows off the tips of the fins.
  • a is the root diameter at the base of the fins
  • b is the radial height of the fins
  • c is the fin spacing or length of tube between fins.
  • the condensing coefficient does not increase proportionately with increasing fin area. This may be explained on the basis that the high but finite thermal conductivity of the metal fins imposes relatively an appreciable resistance to the flow of heat, so that there is a temperature gradient radially through the fins and fin areas further removed from the tube cannot be as effective as fin areas closer to the tube.
  • the fins can be assumed to be perfect conductors, in this spe cial case of condensing nitrogen at low temperature differentials it was found that the thermal gradient in the fin becomes a large enough part of the total condensing resistance to limit the effectiveness of fins higher than about 0.5 cm. for dimension b.
  • an important factor not included in Nusselt's Law has been discovered to be the ratio of the fin height to its average thickness. For nitrogen, we have found the optimum range of such ratio to be between 3 and 4 and a useful range between 3 and 5.
  • a finned tube may be considered as a series of short tubes with the condensate stripped off by each fin.
  • the spacing between the fins at their base may be taken as the tube length L of Nusselt's Law.
  • the condensing coefficient improves when the finned tube is tipped from the vertical to an inclined position which promotes draining of the condensate away from the tube and off the fins.
  • a condenser with 45 inclined tube is shown in FIG. 3 and may be preferred for fabrication, any appreciable angle of inclination down to horizontal will give'higher efficiencies than the vertical position.
  • Thin baffle sheets may be inserted between tube rows to prevent drainage from higher to lower fins in adjacent rows or the lower tubes may be offset or staggered in relation to the upper tubes as illustrated in end view in FIG. 9. Another means for improving drainage is to cut small longitudinal notches or slots through the fins.
  • the fins may be molecularly integral with the tube or thermally metallically bonded thereto and formed by extrusion, rolling, casting, or machining, and the profile can be rectangular or tapered.
  • the rectangular profile is preferred because of slightly higher heat transfer efficiency; however, this form cannot easily be rolled, and hence is less economical for quantity production.
  • FIGS. 6 and 7 illustrate a fin with a included angle between the fin surfaces which is approximately the minimum angle that can be readily rolled. This slight departure from a rectangular profile approaches the latter in efficiency. For example, we obtained an overall coefficient as high as 3,000 B.t.u./hr./sq. ft./F. on a laboratory scale model using specially machined rectangular profile finned tubes. A coefficient of approximately 2,000 B.t.u./hr./sq. ft./F. was obtained on a large commercial scale test using the tapered profile type finned tubes manufactured in a manner suitable for quantity production.
  • the above-described finned tube with optimum dimensions is thus seen to provide an effective means for increasing the nitrogen condensing coefficient of an air separation plant reboiler-condenser.
  • the apparatus When combined with the porous surface which increases the oxygen boiling coefficient, the apparatus produces an overall heat transfer coefficient which is at least 13 times that obtained by the reboiler-condenser customarily in use.
  • the most widely used air separation plant reboiler is known as the Kestner-type condenser.
  • this may comprise 25,000 individually installed 5-ft. long tubes with nitrogen condensing on the outside of the tubes and oxygen boiling on the inside with a percolating effect.
  • Overall heat transfer coefficients for the Kestner condenser are in the range of l00l50 B.t.u./hr./sq. ft./F. at overall temperature differences of 4-10 F.
  • our tests show that with the porous boiling surface-finned condensing surface tube according to this invention, an overall coefficient of approximately 2,000 B.t.u./hr./sq. ft./F.
  • the diameter of the reboiler may be reduced at least 50 percent and the number of tubes reduced to about 5 percent of the number required for the Kestner unit.
  • the overall cost of a reboiler may thus be reduced to about 64 percent of the cost of a conventional Kestner apparatus.
  • a very important substantial power saving may be realized by virtue of the smaller overall temperature differential.
  • FIG. 10 Only two heat exchange units are shown in FIG. 10 and these are of the plate ty e each including a flat lower plate 30 above which is a eeply corrugated heat exchange plate 31 having corrugations with relatively sharp angled lower edges 32 that depend close to but preferably do not touch the plate 30.
  • the plates are sealed by members 33 joining their edges to form a passage between plates 30 and 31 for the condensing vapor such as nitrogen.
  • the upper surface of the corrugations of plate 30 is provided with the porous surface layer 34 according to the invention over which the boiling liquid flows such as oxygen.
  • the nitrogen may be flowed lengthwise of the corrugations while the oxygen may be flowed crosswise as indicated by the arrows.
  • the oxygen passes are provided by the space between the porous surface coated corrugations and the lower plate 30 of the next higher unit and for the upper unit by a flat plate 36 thereabove.
  • the nitrogen condensate draining from the corrugations flows along the top surface of the flat sheet and off at one side due to a preferred slight inclination of the apparatus.
  • porous boiling surface and heat exchange unit Although the low-temperature uses of the porous boiling surface and heat exchange unit according to the invention have been emphasized, experiments show that the improvements' are also advantageous at room temperature and elevate temperature operations.
  • one such porous boiling surface layer was used to boil fluorotrichloromethane (boiling point of 73.8" F.) and was found very efficient.
  • overall coefficients on the order of 2,000 B.t.u./hr./sq. ft./F. were obtained, which can be compared with conventional design evaporator coefficients of about 300 B.t.u./hr./sq, ft./F.
  • the unfinned porous surface unit represents a fivefold advantage.

Abstract

A TUBE-TYPE HEAT EXCHANGER HAVING A POROUS LAYER BONDED TO ONE WALL AND CONSTRUCTED OF THERMALLY CONDUCTIVE PARTICLES INTERGRALLY BONDED TOGETHER TO FORM INTERCONNECTED PORES OF CAPILLARY SIZE.

Description

United States Patent [72] lnventor Robert M. Milton Chappaqua, NY. [21] Appl. No. 46,291 [22] Filed June 15, 1970 Division of Ser. No. 717,691, April 1, 1968, Patent No. 3,523,577, which is a Division of Ser. No. 366,853, May 12, 1964. Patent No. 3,384,154, which is a continuation-in-part of Ser. No. 849,608, Oct. 29, 1959, abandoned, which is a continuation of Ser. No. 607,233, Aug. 30, 1956, abandoned; said Ser. No. 366,853 is a continuation-in-part of Ser. 190.849.665, Oct. 29, 1959. abandoned, which is a division of said Ser. No. 607,233 [45] Patented June 28, 1971 [73] Assignee Union Carbide Corporation [54] HEAT EXCHANGE SYSTEM WITH POROUS BOILING LAYER 3 Claims, 10 Drawing Figs.
[52] U.S.C1 165/110, 62/527, 165/133, 165/166, 165/181 [51] Int. Cl F281'3/02, F28b 1/02 Condensate Primary Examiner-Albert W. Davis, Jr. Attorneys-Paul A. Rose, l-larrie M. l-lumphreys, Leo A. Plum and John C. Le Fever ABSTRACT: A tube-type heat exchanger having a porous layer bonded to one wall and constructed of thermally conductive particles integrally bonded together to form interconnected pores of capillary size. I
" sum 1 OF 5 9 W smuvu Ewod umvmnoa \i HYVItKWU/L gs ROBERT M.MILTON PATENTED JUH28 |sn SHEET 3 OF 5 &
Tyn
nfi xix PATENTED JUH28|971 sum u or 5 ROBE PATENTEUJUHZSIHYI 3,587,730
sum 5 OF 5 ROBERT M.MILTON a continuation of application Ser. No. 607,233 filed Aug. 30,
1956. Application Ser. No. 366,853 is also a continuationinpart of application Ser. No. 849,665 filed Oct. 29, 1959. which in turn is a division of the previously referenced application Ser. No. 607,233. The remaining applications with the exception of Ser. Nos. 366,853 and 717,691 are now abandoned. 1
This invention relates to the art of improving heat transfer from heated surfaces to boiling liquids.
The transfer of heat at effective rates from a heated surface to a boiling liquid in contact therewith ordinarily requires a substantial temperature difference between the surface and the liquid which greatly affects the efficiency of heat transfer. One important factor controlling this efficiency is the nature of the heated surface in contact with the liquid; it being known, for example, that smooth boiling surfaces produce low heat transfer coefficients on the boiling side. Low boiling heat transfer coefficients often severely restrict the heat transfer capacity of boiling apparatus. For example, when the heat for boiling is supplied by a vapor condensing on a smooth-Walled heat transfer surface, the condensing heat transfer coefficient may easily be on the order of 2,000 B.t.u./hr. sq. ft. F., while the boiling heat transfer coefficient against the opposite of the heat transfer surface may be only 100 to 200 B.t.u./hr. sq. ft. F. According to the familiar method of summing heat transfer resistances when the boiling and condensing heat transfer surfaces are of equal area, the overall heat transfer coefficient U is obtained approximately as follows:-
obtained with conventional smooth or roughened surfaces; to-
provide a porous boiling surface layer of a character that is able to transfer to a boiling liquid large quantities of heat at much lower temperature differences than required in conventional heat exchange apparatus; to provide a method of boiling a liquid which has substantially higher heat transfer coefficients at low temperatu're differences; and to provide a method of producing such a porous layer boiling surface on a heat exchange unit.
These and other objects and novel features of the invention will become apparent from the following description and accompanying drawing, in which:
FIG. I is a curve which compares the properties of the porous boiling surface layers of this invention with the surfaces of the prior art.
FIG. 2 is a series of curves comparing the pool boiling performance of the porous boiling surface layers of this invention with the surfaces of the prior art.
FIGS. 3-4 are sectional views in elevation of an exemplary plate-and-fin type heat exchanger illustrating embodiments of the invention.
FIG. 5 is a sectional view in elevation of an exemplary condensing surface embodying the invention.
FIG. 6 is a view partly in elevation and partly in section of an exemplary boiling surface and condensing surface element in the form of a condenser-evaporator tube member embodying the invention.
FIG. 7 is a fragmentary enlarged view in section of a portion of the tube unit.
FIG. 8 is a view showing a preferred inclined arrangement of a condenser-evaporator tube according to the invention.
FIG. 9 is a fragmentary end view of a preferred arrangement of such tubes when mounted in groups.
FIG. 10 is a perspective view of an alternative construction of evaporator-condenser units embodying the invention.
According to the invention, there is provided a porous boiling surface layer having a multitude of small pores bonded on a thermally conductive wall of a heat exchange apparatus for transferring heat to a liquid. The porous boiling surface layer is formed of thermally conductive particles integrally and. thermally bonded together to provide interconnected pores of capillary size within the porous boiling surface layer. The pores are provided in great number per unit area with little nonporous material between them. The porous boiling surface layer is characterized by pronounced capillarity which is described in detail subsequently.
Because of the high boiling heat transfer coefficients produced by the porous boiling surface layer, the temperature difference between a boiling liquid and its source of heat may be substantially reduced while nevertheless achieving a remarkably high rate of heat transfer. Porous boiling surface layers of this invention have been found particularly advantageous in systems requiring elevated pressures to achieve a necessary temperature difference; for example in the reboiler-condenser tubes of a low temperature air separation plant wherein the more volatile normally lower temperature boiling nitrogen gas is condensed by boiling less volatile oxygen liquid, the nitrogen being sufficiently pressurized to raise its condensing temperature above the oxygen boiling temperature. By using a porous boiling surface layer of the present invention, the necessary pressure differential between the fluids may be reduced and power costs minimized.
The preferred procedure for producing a satisfactory porous boiling surface layer comprises sintering, soldering, brazing, or otherwise thermally bonding a layer of fine particles to the base heat transfer surface to form interconnected pores therein having an equivalent pore radius less than about 6.0 mils. As used in this context, the equivalent pore radius" empirically defines a porous boiling surface layer having varied pore sizes and nonuniform pore configurations in terms of an average uniform pore dimension.
An important function of the porous boiling surface layer of this invention is to increase the boiling heat transfer coefficient. In the well-known heat transfer equation Q/A==hAT, the porous boiling surface layer markedly increases the value of the coefficient h. The effect of the increase in this coefficient can be utilized in several ways. The total quantity of heat transferred Q may be increased, the area A may be decreased, the AT may be reduced, or various combinations of these benefits may be realized. I
Since the invention improves the coefficient h, it is distinct from prior art uses of porous elements and devices known as ebullators" which are commonly suspended or immersed in the boiling liquid to reduce superheat and to bring the bulk liquid temperature more nearly in equilibrium with the liquids vapor pressure. Ebullators are often nonmetallic materials such as pumice which contain relatively large random-size pores, only a few of which need be active. The task of the ebullator is relatively easy and simple because the sensible heat represented by a few degrees superheat in the liquid is comparatively small and can be dissipated effectively by a modest degree of boiling. The suspended ebullator material need not be thermally conductive since it does not transfer heat to the liquid. The heat required for boiling on an ebullator surface is transported to that point by the liquid itself in the form of superheat. Thus, while a suspended ebullator may reduce the bulk superheat of the liquid substantially, some degree of liquid superheat must exist in order for boiling to take place on the ebullator.
In contrast to the ebullator art. the porous boiling surface layer of this invention is disposed on the hot wall of the boiling device between the hot wall and the liquid to be boiled and its material must be thermally conductive. lts task is the more difficult one of transferring a very large quantity of heat with a greatly reduced heat flow resistance, i.e. with a reduced temperature difference between the warm wall and the liquid. This temperature difference between the warm wall and the saturated liquid, which is a measure of the heat flow resistance, is the AT which appears in the standard heat transfer equation. lts reduction is achieved herein by the increased heat transfer coefficient ofthe porous boiling surface layer.
Even if materials constructed according to accepted ebullator practice are disposed against the warm wall, they will not achieve the superior results of this invention. To be effective, the porous surface must meet special limitations on the equivalent pore radius as defined hereinafter.
The extreme thinness of the liquid film within the pores is thought to account in large part for the striking improvement in heat transfercoefficient achieved with this invention. It has been discovered that this is an effect which assumes significant proportions only in very small pores, and it is not significant in ebullators designed primarily to reduce superheat. The performance of ebullators is both described and predicted by the combination of the well-known Gibbs and Clapeyron equations which relate the thermal potential required for growth of a bubble (in terms of the superheat of the liquid surrounding the bubble) to the size ofthe bubble:
where r, cavity radius (interchangeable with the equivalent pore radius r of the porous boiling surface layers ofthe present invention, ft.
Also the approximate radius of a bubble emerging from a cavity of radius r a Surface tension, lbs. force/ft.
T =Temperature of liquid surrounding a bubble, "R.
T; Saturation temperature of boiling liquid corresponding to the vapor pressure of the liquid, "R.
Density ofliquid, lbs. mass/ft.
p Density of vapor, lbs. mass/Ft.
It Latent heat of boiling liquid, B.t.u./lb.
The value ofT must be greater than T by an amount sufficient to cause a bubble of radius r, to grow against surface tension. Hence TT is the minimum superheat required to sustain the boiling process. According to the Gibbs-Clapeyron equation, the superheat necessary for bubble growth is reduced, i.e. TT is minimized, by increasing r, and hence an ebullator should be constructed with a porous surface having pores as large as possible which can still retain the entrapped gas or vapor needed to activate the nucleation cites. In FIG. 1, Curve A plots r, vs. the superheat AT necessary to sustain bubble growth, i.e. TT according to the Gibbs-Clapeyron equation for fluorotrichloromethane boiling in contact with surfaces of various pore size with a heat flux of 1,000 B.t.u./hr. sq. ft. In keeping with the objective of ebullators to reduce the required superheat, the performance of a good ebullator would'fall on the portion of Curve A corresponding to low values of AT and high values of r, Tests show that this is in deed true since the values of r, measured for materials con structed as ebullators are between about 8 and I5 mils. The superheat AT corresponds to such pore radii is below 0. 1 F.
However, if one wishes to take a step beyond the phenomenon of the ebullator and to improve overall boiling performance, it will not be sufficient merely to reduce the superheat required to sustain bubble growth. When boiling proceeds by the formation of bubbles within pores or cavities ofa surface which comprises a heat source, the superheat AT, TT correlated by the Gibbs-Clapeyron equation has been discovered to be only one of the resistances to the overall boiling process. A second AT exists across the liquid film between the wall temperature T and the superheated vapor-liquid interface temperature T, and in effect this film AT is in series with the superheat AT of the Gibbs-Clapeyron equation. This film AT, i.e. T rT, has been unexpectedly found to increase as r increases, an effect opposite to that observed for the superheat AT TT The difference between Curves A and B of FIG. 1 depicts this film AT.
Neglecting the thermal resistance of the material of which the surface is composed, the overall boiling process is dependent upon the total AT, T -T which is approximately the sum of the film and superheat ATs. Thus, the sum of the two yields Curve B corresponding to the experimental data of Table I. It is seen that a regime exists at the minimum of Curve B where very low total AT is required to sustain the rate of boiling and where values of r are distinct from the pore dimension of common ebullators. If common ebullators (having a pore radius of 8-10 mils) were coated on the heat transfer wall their performance would not be predicted by Curve A (the Gibbs-Clapeyron curve) because that curve does not take into account the thermal potential required to transfer heat to the liquid-vapor interface surrounding the bubbles. FIG. 1 shows that whereas ebullator coatings might reduce the required superheat AT (Curve A) to a very low value, the coincident filmAT is very high and exerts an overwhelming influence.
The porous boiling surface layers of this invention are unique in that they effectively reduce the film AT and are therefore characterized by performance at the minimum'portion of the curve where the film AT begins to lose its dominant influence and where values ofr are below 6 mils. In preferred practice, the equivalent pore radius, r should be below about 4.5 mils.
Curves A and B of FIG. 1 represent the results obtained with fluorotrichloromethane as described above. Other liquids will provide similar curves, which due to the individual pro-- perties of each liquid will be, in general, displaced along the abscissa. For all such liquids, however, a porous boiling surface layer constructed according to the present invention will have an equivalent pore radius of less than about 6.0 mils and preferably less than about 4.5 mils.
FIG. 2 shows in an even more striking manner the distinctive groupingof the porous boiling surfaces apart from conventional surfaces. The surfaces tested correspond to those listed in Table I and the curves are numbered accordingly. Prior art boiling surfaces have not approached the extremely high coefficients (heat flux per unit AT) which are obtained in this invention as exemplified by FIG. 2.
The equivalent pore radius of a porous boiling surface layer is most conveniently and accurately determined by vertically immersing one end of the porous boiling surface layer in a freely wetting liquid and measuring the capillary rise of the liquid along the surface of the porous boiling surface layer. When determined in this manner, the equivalent pore radius, r, is equal to 2cr/ph where: p is the density (in lbs. mass/cu. ft.) of the liquid in which an end of the porous boiling surface layer is vertically immersed: ois the surface tension (in lbs.
force/ft.) of the liquid in which an end of the porous boiling surface layer is vertically immersed; and h is the vertical capillary rise (in ft.) of the liquid along the surface of the porous boiling surface layer.
The advantage in choosing a freely wetting liquid to determine the equivalent pore radius is that the liquid phase contact angle (0), which the liquid surface makes with the materials of which the porous boiling surface layer is composed, will be very small and, therefore, will not effect the determination. If a freely wetting liquid is not chosen, the expression 2o'lph must be equated to r/cos 0 and the contact angle (6) will have to be accounted for in determining the value of the equivalent pore radius (r). Since the exact measurement of the contact angle is difficult and unnecessarily introduces risk of error, it is preferable to use a freely wetting liquid to determine the equivalent pore radius. Liquids exhibiting a contact angle of less than 20 with the material of which the porous boiling surface layer is composed are defined as "freely wetting" for this purpose and may be used without having to account for the effect of the contact angle since cos 20 is 0.95 and the error resulting from neglecting the contact angle will be less than 5 percent.
Examples of suitable liquids which freely wet aluminum and copper surfaces (two of the preferred materials for constructing porous boiling surface layers) are methanol, fluorotrichloromethane, dichlorotetrafluoroethane. acetone, ethyl chloride, liquid oxygen and liquid nitrogen. The particular liquid chosen for determination of the equivalent pore radius should preferably be a good solvent for oil and grease so that the effect of the presence of these common surface contaminants will be minimized. Pure water is not considered to be a freely wetting liquid inasmuch as its contact angle (0) with an aluminum surface, for example, is about 66.
The equivalent pore radius is independent of the properties of the material used to construct the porous boiling surface layer. It defines qualitatively the geometrical and dimensional characteristics of the porous boiling surface layer itself. The equivalent pore radius should not be employed to predict the quantitative performance of any particular porous boiling surface layer inasmuch as such performance will depend, inter alia, on the material of which the porous boiling surface layer is constructed and the liquid which is to be boiled.
Table I, column 2, summarizes the values of the effective pore radius determined experimentally for a number of surfaces including prior art ebullators as well as porous boiling surface layers of the present invention in freely wetting liquidsspecifically methanol, fluorotrichloromethane, and dichlorotetrafluoroethane. Column 3, of Table I, shows the values of temperature differences required by the several surfaces to transfer 1,000 B.t.u./hr. sq. ft. while boiling fluorotrichloromethane. Since Q/A is held constant at l,000, the only variable in the heat transfer equations are AT and h, and these variables are inversely proportional. Consequently, a decrease in the required AT by a factor of will increase the heat transfer coefficient h by a factor of l0. Thus, column 3 of Table l provides a means of comparing the heat transfer capabilities ofthe various surfaces in a common fluid.
TABLE I AT F.) Equivalent required for pore radius, Q/A=1,000 Surface in mils B.t.u./hr.sq.ft
Porous Boiling Surface Layers:
1. Copper, 325 mesh spherical. fiat p te 1. 65 0.83 2. Copper, 325 mesh granular,
cylinder 1. 67 1.10 3. Aluminium, 40-100 mesh granular,
flat plate 3. 44 1. 20 4. Copper, 35-60 mesh spherical flat plate-... 3. 41 1. 5. Aluminum, 80- ar,
flat plate 3. 0 1. 33 Metallic Ebullators:
6. Mossy Zinc Ebullator 10. 0-15. 0 5. 0 7. Antimony cbullator, granular 8.0 5.1 Smooth Surfaces:
8. Smooth copper plate 8. 8 9. Smooth aluminum plate 14. 0 Non-metallic Ebullator:
10. Sodium Silicate cbullators 16. 6 16.6
1 Exhibits no capillarity.
1 Non-porous.
A porous boiling surface layer, as described above, in operation provides a multitude of interconnecting partially liquid filled capillaries which act as nuclei for the growth of many bubbles of the boiling liquid lf the pores were not interconnected, their continued performance as nuclei for bubble growth would be critically dependent upon retaining entrapped air or vapor within the pores. However, with interconnected pores, vapor formed in one pore can activate one or several adjacent pores, so that the process continues without interruption and without dependence upon air or vapor entrapment. At least some of the pores in the interconnected matrix are also believed to supply liquid to adjacent pores. As the bubbles grow, they finally emerge from the interconnected capillaries, due to continued generation of vapor within the capillaries, break away from the surface, and rise through the liquid film covering the porous boiling layer. The liquid continues its flow into the capillaries and maintains the capillary walls wet, thus giving increased surface evaporation. The high boiling coefficient results from the fact that the heat leaving the base metal surface does not have to travel through an appreciable liquid layer before meeting a vapor-liquid surface producing evaporation.
Within the porous boiling surface layer, a multitude of bubbles are grown so that the heat, in order to reach a vaporliquid boundary, need travel only through an extremely thin liquid layer having a thickness considerably less than the minute diameter of the confining pore. vaporization of liquid takes place entirely within the pores and substantially no superheating of the bulk liquid is requiredorcan occur.
With a smooth metal surface, however, only a few bubble points exist and the initiation of bubble growth requires a large degree of superheat due to the compressive force of liquid surface tension on a very small bubble. The heat for bubble growth must be transferred by convection and conduction form the smooth base metal to the distant vapor-liquid interface of a bubble which is almost completely surrounded by bulk liquid.
The above-described performance of a porous boiling surface layer is not merely the result of increasing the surface area by, for example, mechanically roughening the surface.
This fact was shown by a test comprising immersing a porous boiling surface layer bonded to a copper block containing embedded heating coils to boil liquid oxygen. At very low .heat fluxes insufficient to activate the pores with vapor, the boiling heat transfer coefficient and the visual phenomena of bubble points were quite similar to those obtained with a smooth surface copper block. However, at higher heat fluxes producing vapor activation of the pores, extremely high boiling coefficients were obtained which are impossible to achieve with the smooth block or with a block having thoroughly mechanically roughened surfaces. The following test results in boiling liquid oxygen illustrate the effect of porous boiling surfaces at three temperature differences, and at heat fluxes sufficiently large to produce vapor activation of the pores.
TABLE II.COEFFICIENTS OF HEAT TRANSFER Tempera- Heat Transfer ture Difier- Coeflicient ence Cal./ C. B.t.u./hr Type Surface C. F. em. sec. sq. ft-
Smooth copper 0 5 0.9 0.01 74 Mechanically roughened coppen. 0.02 148 Sintei'ed nickel 1 0. 18 1, 330 Sintered copper 1 0. 50 3, 690
Smooth copper 1. O 1.8 0. 013 96 Mechanically roughened copper 0. 034 251 Sintered nickel l 0. 28 2. 060 Slntered copper 1 2.83 6,
Smooth copper 1. 5 2. 7 0. 046 340 Mechanically roughened copper 0. 046 340 Sinteted nickel l O. 32 2, 360 Sintered copper exceeded 1. 0 7, 400
1 Porous boiling surface layer of present invention.
,Value too large to be measured in test equipment.
Table 11 indicates that by using a porous boiling surface of this invention, even a metal such as nickel exhibits boiling coefficients far greater than those obtained with conventional surfaces of highly conductive copper, despite the fact that the conductivity of nickel is only one-sixth that of copper.
To illustrate the method of determining the equivalent pore radius, consider the following data and computation for item 1 of Table l and of FIG. 2. A small strip of copper sheet with the porous surface applied thereon was suspended vertically with one end immersed in fluorotrichloromethane. The liquid wetted the surface by capillary action to a height h above the liquid surface of0.2l ft. Fluorotrichloromethane has a surface tension of l.30 l' lbs/ft. and a density of 91.4 lb./cu. ft. Substituting these values into the equivalent pore radius equation gives a value for r ofO. l 38X l0 ft. or 1.65 mils.
The powder particles used in preparing the porous boiling surface are preferably either granular or spherical. Geometrical considerations suggest that granular or spherical particles are more effective than flakes in producing a large number of approximately uniform sized pores. Very thin flakes are less desirable since they are difficult to bond as discrete particles, and because their extremely large surface area complicates the task of cleaning the powder thoroughly A comparison of items 1 and 4 (spherical) with items 2, 3 and 5 (granular) in Table I and FIG. 2 shows that both granular and spherical particles produce excellent surfaces. with spherical particles showing some advantage.
In general, any metallic material is suitable for preparing the porous boiling surface, provided it has good thermal conductivity, is available as a fine powder, is bondable to itself and to the base metal, and is easily wetted by the liquid to be boiled.
The particle material should preferably have high thermal conductivity as stated previously. Among others, nickel and copper porous boiling surface layer materials on copper base metal have been tested under identical conditions; the copperon-copper heat transfer coefficient being about three times as large as the nickel-on-copper combination which is to be ex pected because of the higher thermal conductivity of copper. Further evidence of the desirability of high thermal conductivity is seen in FIG. 2 where the performance of fine-mesh copper surfaces (curves 1 and 2) is better than fine-mesh aluminum surface (curve 3). The conductivities of copper and aluminum are 224 and 117 B.t.u./hr. sq. ft. F./ft., respective ly. ln corrosive service, alloys, such as stainless steel, resistent to chemical attacks may be used.
The optimum thickness of the porous boiling surface is only slightly affected by the physical properties of the boiling liquid. This is indicated by tests wherein high boiling heat transfer coefficients are obtainable in stream-water service from a porous boiling surface having a thickness previously determined as optimum for oxygen service. The thickness of the porous boiling surface layer may vary by at least a factor of 10 without severe detriment. The thickness should be greater than the average particle diameter and preferably should be at least twice the average particle diameter. With fine particles such as 323 mesh, uniformity and complete continuity of the coating will usually govern the minimum thickness which is applied. A practical minimum thickness is about 0.1 mm.
Functionally, the maximum thickness which can be used without detriment is controlled only by the capillarity of the surface and by the ability of the surface to discharge the vapor produced in boiling. in operation, the surface should be capable of drawing the liquid all the way through the thickness to the base metal so that the surface is completely wetted, while at the same time discharging and disengaging the vapor from the pores. Excellent results have been obtained with relatively thick surfaces; for example, the porous boiling surface layer of item 1 ofTable l and ofFlG. 2 is 0.25 mm. thick.
The relationship between particle size and performance of a porous boiling surface layer is not exact. Tests show that excellent porous boiling surfaces can be formed of powder having very fine granular or spherical particles l50 microns in size. Such porous boiling surfaces have exhibited very high boiling heat transfer coefficients in tests with liquid oxygen and with water. However, other tests indicate that there is very little performance difference in boiling liquid oxygen between porous boiling surfaces produced from fine powder, e.g. screen analysis showing a major portion (98 percent) passing through 325 mesh (98 percent 44 microns), and coarse powder, e.g. 50-60 percent passing through 100 mesh (50- 60 percent 150 microns). If present in sufficient number, the smaller particles determine the pore dimensions since they will fill the voids between the large particles.
A suitable porous surface according to the invention may be produced by sintering l to 50 micron-size particles of a heat conductive metal such as copper to the hot wall supplying heat to the boiling liquid. The particles are applied in such quantity to provide a porous layer thickness between about 0.l mm. and 1.0 mm. The interstices or voids between the particles should be essentially free of solid material and should be interconnected within the depth of the layer. The interconnected pores thus formed will be between about 1 micron and microns in size and there will be a great number per unit area of surface.
In selecting the powder for surface preparation, one should be guided by the fact that the equivalent radius of the pores of the porous boiling surface layer is the critical factor and that particle size alone is not necessarily determinative. As indicated above, the particle size distribution within the range of sizes present in the sample will also influence the pore size. Particle shape will have an effect since spheres, for example, will stack more compactly than irregular shapes and will produce smaller voids. The innumerable variations which these factors permit makes it impractical to bracket all suitable powders within a single specification. For this reason, the equivalent pore radius determined by routine testing on specimens of the finished porous boiling surface layer as described previously is technically a more accurate method of identification.
Various methods for producing a sintered metal porous boiling surface on a base metal may be employed. One preferred method is to use a temporary binder such as a plastic material to establish and maintain a uniform coating on the base metal surface, the binder being such that it decomposes and vaporizes during the heating and sintering process. One such plastic is an isobutylene polymer having a molecular weight of about 140,000 and known commercially as The plastic binder is dissolved in an appropriate solvent such as kerosene or carbon tetrachloride and sufficient metal powder is added to give a uniform viscous slurry with a metalplastic weight ratio of about 92 to 1. The base metal surface must be free of grease, oil and oxide coating to obtain proper bonding of the porous coating. Just before applying the slurry, the surface may be flushed with the plastic solution to facilitate wetting by the slurry, thereby obtaining more even distribution.
A number of methods may be used for applying a slurry coating to the base metal. The object is to achieve a uniform coating, and the selection of the method will depend upon the geometry and orientation of the surface. Spraying and dipping are two procedures which have been used successfully.
The coating is air dried either during or after the application procedure. The bulk of the solvent is thus removed by evaporation leaving a solid, self-supporting layer which is held in place by the binder. Then the base metal and the coating are blanketed with a mildly reducing atmosphere and the temperature is raised for a sufficient time to sinter the particles together and to the base metal. The circulating reducing gas removes the thin oxide film and also purges the decomposition products from the surface materials. In the case of copper, the coating is sintered at about F. below its melting point, or about 1,760 F.
Another successfully employed binder is a methyl cellulose polymer having a viscosity of 4,000 c.p.s. and known commercially as Methocel. A preferred slurry comprises 32 grams of copper powder in l00 cc. of a 2 percent water solution of such polymer. After application of a coating of the slurry on the base metal, it is air dried at ordinary temperatures (below the boiling point of water), and then furnace dried at about 750 F. in an atmosphere of water saturated annealing gas. The coating is then sintered at appropriate sintering temperatures.
Still another plastic binder which is successfully used in polystyrene which has a molecular weight of about 90,000 and is soluble in toluene or xylene.
As stated above, binders and slurries are used to facilitate distribution and to hold the powder temporarily in place until a permanent thermal bond can be achieved. When surface arrangement permits the powder may be applied and sintered in dry form; for example, the surface reported as item 1 in Table land FIG. 2 was prepared in this manner.
One arrangement consists of applying the porous boiling surface on the inner wall of heat exchanger tubes. For such arrangement, an excellent procedure is to preliminarily distribute the slurry within the length of the tube, and then place the tube in a machine capable of rotating the tube about its own axis at a rate sufficient to produce a smooth coating, about 200 r.p.m. The coating is air dried during the spinning operation and is then furnace sintered under the conditions previously described.
Another application procedure lends itself particularly to flat, corrugated or outside-cylindrical surfaces. According to this method, a slurry of metal powder and plastic binder is fed from a hopper'onto the outer surface of a polished roll in a uniform layer. As the roll slowly rotates, the evaporation of the vehicle sets the plastic film and the latter is continuously stripped off the roll as a sheet of the plastic material containing the embedded metal powder. The composite film is then placed in contact with the surface of a metal sheet which is conducted into the furnace wherein the plastic is vaporized and the metal powder sintered to the sheet. This process lends itself very readily to quantity production methods.
One preferred construction of a heat exchange apparatus employing a porous boiling surface layer is shown in FIG. 3. This apparatus is a plate-type heat exchanger comprising a plurality of fluid passes defined by parallel, spaced parting sheets housed in a core section with appropriate headers and manifolds for the fluid streams. As shown in FIG. 3, thermally conductive metal walls in the form of parting sheets 1 and 2, which define the fluid pass 3 for the boiling liquid are'coated with a porous boiling surface layer 4, the fluid passes on either side offluid pass 3 being provided for the warm fluid supplying heat to vaporize the liquid within the pores of the porous boiling surface layer. Protrusions 9 and from the parting sheets are in registry and abut with one another to form stays between the passage walls.
FIG. 4 shows another preferred construction for boiling condensing service using a flat plate type heat exchanger with corrugated fins in the passages. The boiling passage is formed between parting sheets 1 and 2 and contains fin material 5 with corrugations widely spaced, e.g. 6 per inch. All exposed surfaces in the boiling passage are shown coated with porous boiling surface layer 4. The condensing passage is formed between parting sheets 2 and 3 and contains fin material 6 with corrugations closely spaced, e.g. 25 per inch. The closely spaced fins provide high surface area and distribute the condensate in a thinner layer of lower heat flow resistance. This increase h A with respect to h A, and brings these factors into balance.
To take maximum advantage of the increased boiling heat transfer coefficient achieved by use of porous boiling surface layers in apparatus utilizing a condensing fluid as a heat source, it is desirable to provide special condensing surfaces which permit achieving a high condensing heat transfer coefficient. FIG. 3 also shows such a condensing surface constructed in the form of very fine corrugations 6 which permit condensed liquid to be drawn by surface tension to the valleys 7 of the corrugations leaving the crests 8 stripped of all but a thin layer of liquid as shown in FIG. 5. The utility of a condensing surface such as shown in FIG. 5 is not limited to plateand-fin type heat exchangers such as shown in FIG. 3. For example, such a surface may be applied to the exterior surfaces of tubes in shell-and-tube type heat exchangers where a porous boiling surface layer is bonded to the interior surface of the tubes.
Referring to FIG. 5, a condensable vapor contacts the corrugated surface 6 and forms a condensate film thereon. The film, or more precisely the vapor liquid interface, acts as a membrane which is stretched elastically by surface tension over the crests of the corrugations. Therefore, the pressure in the liquid under the interface in the arc of each crest is greater than the pressure of the vapor above the interface. In the valleys 7, the curvature of the liquid-vapor interface is reversed and the tension therein produces the opposite efiect; the pressure in the liquid is less than the pressure of the vapor. Because the pressure exerted by the interfacial membrane is greater in the crest area than in the valley area, the condensate flows into the valley leaving a very thin film over the crest. Once in the valleys, the condensate flows parallel to the valleys (normal to the plane of FIG. 5) under the force of gravity to a suitable manifold means where it is withdrawn from the condensing surface.
If the crests and valleys are too wide, the radius of curvature of the interfacial membrane will be large and the surface tension effect small. If the corrugations are too shallow, the valleys will have insufficient liquid-holding capacity and the crest area will flood. If the corrugations are too deep, the effectiveness of the interfacial membrane tension in the crest area will be reduced. Satisfactory dimensions must be designed with consideration of the condensing-liquid density, viscosity, surface tension, and the like. Usually, the valley 7 and crest 8 of the corrugations would have semicircular cross sections with radii between about 0.005 and 0.015 inches.
FIGS. 6 and 7 of the drawings show another embodiment of the present invention comprising a thermally conductive metal tube 10 which is provided on its internal boiling surface 11 with a porous boiling surface layer 12 formed of metal powder particles sintered to each other and to the inside surface of the tube 10. The outer surface of the tube is preferably provided with fins or flanges 13 metallically bonded or molecularly integral with the tube 10 for most efficient heat conduction. In one organization, a plurality of such finned tubes is mounted between headers in areboilengopdenser portion of an apparatus for air separation by low-temperature rectification into its primary constituents oxygen and nitrogen wherein gaseous nitrogen at approximately 60-l00 p.s.i. is condensed on the finned outer side of the reboiler tubes, and liquid oxygen at approximately 0--l5 p.s.i. is boiled in the porous surface coated inside of the tubes. The heat required to boil the liquid oxygen is transferred from condensing nitrogen and radially inward across the fins and through the metal wall to the boiling oxygen. The ends of the tube unit may be constructed for mounting in openings, tube headers being preferably expanded to a larger diameter as shown at 14 and 15.
In FIG. 8, for clearness of illustration, only one tube unit 10 is shown mounted between headers 16 and 17 which seal off lower and upper portions of a condenser casing 18, the tube ends 14 and 15 being secured gas-tightly in corresponding openings of the headers. The casing ends are capped at 19 and 20 to form inlet and outlet chambers for liquid to be boiled, such as oxygen supplied through a conduit 21 and for collection of the resulting vapor which is led off by a conduit 22. The vapor, such as cold nitrogen to be condensed is conducted to an upper part of the casing 18 through a connection 23, and the resulting condensate, liquid nitrogen, may be led off through a lower connection 24. In practice, as many tubes 10 as are required are mounted between headers of suitable size.
Some geometric similarity may be noticed between FIGS. 5 and 7, but functionally they are quite different. As stated above condensate collects by surface tension in the very narrow valleys of FIG. 5 and runs off normal to the view of FIG. 5. In contrast, the fins of FIG. 7 are spaced wider apart so that condensate, tending to flow longitudinally of the tube, is instead diverted or stripped away from the tube and flows off the tips of the fins.
Referring again to FIG. 7 a is the root diameter at the base of the fins, b is the radial height of the fins, c is the fin spacing or length of tube between fins. In condensing service, these dimensions all have an important effect on the condensing heat transfer coefficient, and the following discusses the optimum values which we have found for nitrogen condensation.
It was found experimentally that beyond a certain upper limit of fin height, the condensing coefficient does not increase proportionately with increasing fin area. This may be explained on the basis that the high but finite thermal conductivity of the metal fins imposes relatively an appreciable resistance to the flow of heat, so that there is a temperature gradient radially through the fins and fin areas further removed from the tube cannot be as effective as fin areas closer to the tube. Although in most heat transfer problems, the fins can be assumed to be perfect conductors, in this spe cial case of condensing nitrogen at low temperature differentials it was found that the thermal gradient in the fin becomes a large enough part of the total condensing resistance to limit the effectiveness of fins higher than about 0.5 cm. for dimension b. Furthermore, an important factor not included in Nusselt's Law has been discovered to be the ratio of the fin height to its average thickness. For nitrogen, we have found the optimum range of such ratio to be between 3 and 4 and a useful range between 3 and 5.
A finned tube may be considered as a series of short tubes with the condensate stripped off by each fin. Thus, the spacing between the fins at their base may be taken as the tube length L of Nusselt's Law.
Theoretically it is desirable to use as many fins per unit tube length as possible, but we-have found experimentally that when the fins become too close to each other, surface tension causes the liquid to hold up between fins and prevent further condensation on either fins or tubes.
If this occurs, heat transfer is substantially reduced because of the smaller available surface area for condensing and the increased film resistance. Thus, a balance exists between fin plugging from too closely spaced fins and a decrease of heat transfer values due to excessive fin spacing, and we have found than an optimum range for nitrogen is between 1.5 and 2.2 mm. for dimen sion c although spacings up to 3 mm. are efficient.
It was also found that the condensing coefficient improves when the finned tube is tipped from the vertical to an inclined position which promotes draining of the condensate away from the tube and off the fins. Although a condenser with 45 inclined tube is shown in FIG. 3 and may be preferred for fabrication, any appreciable angle of inclination down to horizontal will give'higher efficiencies than the vertical position. Thin baffle sheets may be inserted between tube rows to prevent drainage from higher to lower fins in adjacent rows or the lower tubes may be offset or staggered in relation to the upper tubes as illustrated in end view in FIG. 9. Another means for improving drainage is to cut small longitudinal notches or slots through the fins.
The fins may be molecularly integral with the tube or thermally metallically bonded thereto and formed by extrusion, rolling, casting, or machining, and the profile can be rectangular or tapered. The rectangular profile is preferred because of slightly higher heat transfer efficiency; however, this form cannot easily be rolled, and hence is less economical for quantity production. FIGS. 6 and 7 illustrate a fin with a included angle between the fin surfaces which is approximately the minimum angle that can be readily rolled. This slight departure from a rectangular profile approaches the latter in efficiency. For example, we obtained an overall coefficient as high as 3,000 B.t.u./hr./sq. ft./F. on a laboratory scale model using specially machined rectangular profile finned tubes. A coefficient of approximately 2,000 B.t.u./hr./sq. ft./F. was obtained on a large commercial scale test using the tapered profile type finned tubes manufactured in a manner suitable for quantity production.
The above-described finned tube with optimum dimensions is thus seen to provide an effective means for increasing the nitrogen condensing coefficient of an air separation plant reboiler-condenser. When combined with the porous surface which increases the oxygen boiling coefficient, the apparatus produces an overall heat transfer coefficient which is at least 13 times that obtained by the reboiler-condenser customarily in use.
The most widely used air separation plant reboiler is known as the Kestner-type condenser. In a large oxygen plant, this may comprise 25,000 individually installed 5-ft. long tubes with nitrogen condensing on the outside of the tubes and oxygen boiling on the inside with a percolating effect. Overall heat transfer coefficients for the Kestner condenser are in the range of l00l50 B.t.u./hr./sq. ft./F. at overall temperature differences of 4-10 F. As previously mentioned, our tests show that with the porous boiling surface-finned condensing surface tube according to this invention, an overall coefficient of approximately 2,000 B.t.u./hr./sq. ft./F. is obtainable, and the optimum temperature difference is only 0.6-l.0 F. This means that in addition to increased efficiency, a substantial reduction in both cost and size of an important part of the apparatus can be realized. For example, based on an overall coefficient of 2,000 and a AT of 3.4 F., the diameter of the reboiler may be reduced at least 50 percent and the number of tubes reduced to about 5 percent of the number required for the Kestner unit. The overall cost of a reboiler may thus be reduced to about 64 percent of the cost of a conventional Kestner apparatus. Furthermore, a very important substantial power saving may be realized by virtue of the smaller overall temperature differential.
As previously mentioned in the case ofcondensing nitrogen, a temperature gradient in the fins was found to limit the amount of added condensing surface that can be employed on tubes by increasing the length b of the fins. An alternative construction which avoids such fin temperature drop employs corrugated surfaces as shown in FIG. 10 where ample condensing surface is made available, yet only a thin thickness of metal separates the extended area condensing surface from the boiling surface. Only two heat exchange units are shown in FIG. 10 and these are of the plate ty e each including a flat lower plate 30 above which is a eeply corrugated heat exchange plate 31 having corrugations with relatively sharp angled lower edges 32 that depend close to but preferably do not touch the plate 30. The plates are sealed by members 33 joining their edges to form a passage between plates 30 and 31 for the condensing vapor such as nitrogen. The upper surface of the corrugations of plate 30 is provided with the porous surface layer 34 according to the invention over which the boiling liquid flows such as oxygen. To provide separate passages for the two fluids, a plurality of such units are assembled as shown; and for convenience of providing flow connections, the nitrogen may be flowed lengthwise of the corrugations while the oxygen may be flowed crosswise as indicated by the arrows. The oxygen passes are provided by the space between the porous surface coated corrugations and the lower plate 30 of the next higher unit and for the upper unit by a flat plate 36 thereabove. The nitrogen condensate draining from the corrugations flows along the top surface of the flat sheet and off at one side due to a preferred slight inclination of the apparatus.
Although the low-temperature uses of the porous boiling surface and heat exchange unit according to the invention have been emphasized, experiments show that the improvements' are also advantageous at room temperature and elevate temperature operations. For example, one such porous boiling surface layer was used to boil fluorotrichloromethane (boiling point of 73.8" F.) and was found very efficient. In boiling water tests, overall coefficients on the order of 2,000 B.t.u./hr./sq. ft./F. were obtained, which can be compared with conventional design evaporator coefficients of about 300 B.t.u./hr./sq, ft./F. On the basis of heat transferred per unit volume occupied by tubes, the unfinned porous surface unit represents a fivefold advantage.
This application is a continuation-in-part of copending applications Ser. No. 849,665, filed Oct. 29, 1959 and Ser. No. 849,608, filed Oct. 29, 1959.
I claim:
1. In an exchanger for transferring heat from a warmer fluid to a colder liquid to be boiled having a first passageway adapted to receive said colder liquid and discharge vapor 2. An exchanger according to claim 1 wherein said thin corrugated metal wall is a plate.
3. An exchanger according to claim 1 wherein said thin corrugated metal wall is a plate and said exchanger comprises a multiplicityof superimposed first and second passageways in alternating sequence with each pair of adjacent plate-type thin corrugated metal walls being separated by an intervening flat plate.
US46291A 1956-08-30 1970-06-15 Heat exchange system with porous boiling layer Expired - Lifetime US3587730A (en)

Applications Claiming Priority (6)

Application Number Priority Date Filing Date Title
US60723356A 1956-08-30 1956-08-30
US84960859A 1959-10-29 1959-10-29
US84966559A 1959-10-29 1959-10-29
US366853A US3384154A (en) 1956-08-30 1964-05-12 Heat exchange system
US71769168A 1968-04-01 1968-04-01
US4629170A 1970-06-15 1970-06-15

Publications (1)

Publication Number Publication Date
US3587730A true US3587730A (en) 1971-06-28

Family

ID=27556508

Family Applications (1)

Application Number Title Priority Date Filing Date
US46291A Expired - Lifetime US3587730A (en) 1956-08-30 1970-06-15 Heat exchange system with porous boiling layer

Country Status (1)

Country Link
US (1) US3587730A (en)

Cited By (48)

* Cited by examiner, † Cited by third party
Publication number Priority date Publication date Assignee Title
US3990862A (en) * 1975-01-31 1976-11-09 The Gates Rubber Company Liquid heat exchanger interface and method
US4046529A (en) * 1976-05-21 1977-09-06 Nasa Regenerable device for scrubbing breathable air of CO2 and moisture without special heat exchanger equipment
US4074753A (en) * 1975-01-02 1978-02-21 Borg-Warner Corporation Heat transfer in pool boiling
US4101691A (en) * 1976-09-09 1978-07-18 Union Carbide Corporation Enhanced heat transfer device manufacture
US4129181A (en) * 1977-02-16 1978-12-12 Uop Inc. Heat transfer surface
FR2486627A1 (en) * 1980-07-14 1982-01-15 Cryoplants Ltd HEAT EXCHANGER AND METHOD FOR BOILING LIQUIFIED GAS
EP0053452A2 (en) * 1980-12-02 1982-06-09 Marston Palmer Ltd. Heat exchanger
US4350025A (en) * 1980-04-18 1982-09-21 Nissan Motor Company, Limited Refrigerant evaporator
US4353224A (en) * 1980-10-16 1982-10-12 Nippondenso Co., Ltd. Evaporator
US4381818A (en) * 1977-12-19 1983-05-03 International Business Machines Corporation Porous film heat transfer
WO1986000124A1 (en) * 1984-06-14 1986-01-03 Total Energy Conservation & Management Company Lim Improvements in earth heat recovery systems
EP0236907A1 (en) * 1986-03-11 1987-09-16 Air Products And Chemicals, Inc. Heat exchanger for boiling liquids
US4698135A (en) * 1983-02-10 1987-10-06 Sirdan Research Limited Desalinating drip-irrigation system
EP0303492A2 (en) * 1987-08-14 1989-02-15 The BOC Group plc Liquefied gas boilers
US5752566A (en) * 1997-01-16 1998-05-19 Ford Motor Company High capacity condenser
US5755113A (en) * 1997-07-03 1998-05-26 Ford Motor Company Heat exchanger with receiver dryer
US6082444A (en) * 1997-02-21 2000-07-04 Tocalo Co., Ltd. Heating tube for boilers and method of manufacturing the same
EP1048918A2 (en) * 1999-04-28 2000-11-02 Haruo Uehara Evaporator
US6186222B1 (en) * 1997-07-16 2001-02-13 The Furukawa Electric Co., Ltd Aluminum alloy tube and heat exchanger, and method of metal-spraying a filler alloy
US6340052B1 (en) * 1999-04-28 2002-01-22 Haruo Uehara Heat exchanger
US20020056546A1 (en) * 2000-02-02 2002-05-16 York International Corporation Plate heat exchanger assembly with enhanced heat transfer characteristics
EP1262725A3 (en) * 2001-05-22 2003-01-08 Praxair Technology, Inc. Cryogenic condensation and vaporization system
US6666909B1 (en) * 2000-06-06 2003-12-23 Battelle Memorial Institute Microsystem capillary separations
US20040103660A1 (en) * 2002-02-13 2004-06-03 Ship & Ocean Foundation Heat exchanger applicable to fuel-reforming system and turbo-generator system
US20050229553A1 (en) * 2000-06-06 2005-10-20 Tegrotenhuis Ward E Conditions for fluid separations in microchannels, capillary-driven fluid separations, and laminated devices capable of separating fluids
US20060032242A1 (en) * 2003-01-27 2006-02-16 Tegrotenhuis Ward E Methods for fluid separations, and devices capable of separating fluids
US20070102070A1 (en) * 2005-11-07 2007-05-10 3M Innovative Properties Company Thermal transfer coating
US20070102140A1 (en) * 2005-11-07 2007-05-10 3M Innovative Properties Company Structured thermal transfer article
WO2007100297A1 (en) 2006-03-03 2007-09-07 Richard Furberg Porous layer
US20080023179A1 (en) * 2006-07-27 2008-01-31 General Electric Company Heat transfer enhancing system and method for fabricating heat transfer device
US20080041573A1 (en) * 2003-05-30 2008-02-21 Uop Llc Method for making brazed heat exchanger and apparatus
US20080099191A1 (en) * 2005-02-02 2008-05-01 Carrier Corporation Parallel Flow Heat Exchangers Incorporating Porous Inserts
WO2008078211A1 (en) * 2006-12-20 2008-07-03 Turk Demir Dokum Fabrikalari Anonim Sirketi A heat exchanger
US20080230212A1 (en) * 2004-01-12 2008-09-25 Frederic Crayssac Fin for Heat Exchanger and Heat Exchanger Equipped with Such Fins
US7540475B2 (en) 2005-09-16 2009-06-02 Battelle Memorial Institute Mixing in wicking structures and the use of enhanced mixing within wicks in microchannel devices
US20090321053A1 (en) * 2008-06-05 2009-12-31 Battelle Memorial Institute Enhanced Two Phase Flow in Heat Transfer Systems
US20100059205A1 (en) * 2002-04-29 2010-03-11 Kauppila Richard W Cooling arrangement for conveyors and other applications
EP2291598A1 (en) * 2008-06-30 2011-03-09 Uop LLC Methods of manufacturing brazed aluminum heat exchangers
WO2011154879A3 (en) * 2010-06-08 2012-03-15 Memc Electronic Materials, Inc. Trichlorosilane vaporization system
US20130048261A1 (en) * 2011-08-26 2013-02-28 Hs Marston Aerospace Ltd. Heat exhanger
US20130206368A1 (en) * 2010-10-19 2013-08-15 Nec Corporation Cooling device and method for producing the same
US20150292818A1 (en) * 2012-08-18 2015-10-15 Audi Ag Heat exchanger
US9279626B2 (en) * 2012-01-23 2016-03-08 Honeywell International Inc. Plate-fin heat exchanger with a porous blocker bar
US20160377350A1 (en) * 2015-06-29 2016-12-29 Honeywell International Inc. Optimized plate fin heat exchanger for improved compliance to improve thermal life
US20170276434A1 (en) * 2014-08-29 2017-09-28 Kyungdong Navien Co., Ltd. Air guide-integrated evaporation cooler and method for manufacturing same
US10047880B2 (en) 2015-10-15 2018-08-14 Praxair Technology, Inc. Porous coatings
US10048024B1 (en) 2017-04-26 2018-08-14 Joshua D. Sole Two-phase fluid flow distributor and method for parallel microchannel evaporators and condensers
US10520265B2 (en) 2015-10-15 2019-12-31 Praxair Technology, Inc. Method for applying a slurry coating onto a surface of an inner diameter of a conduit

Cited By (77)

* Cited by examiner, † Cited by third party
Publication number Priority date Publication date Assignee Title
US4074753A (en) * 1975-01-02 1978-02-21 Borg-Warner Corporation Heat transfer in pool boiling
US4093755A (en) * 1975-01-31 1978-06-06 The Gates Rubber Company Method for making a liquid heat exchanger coating
US3990862A (en) * 1975-01-31 1976-11-09 The Gates Rubber Company Liquid heat exchanger interface and method
US4046529A (en) * 1976-05-21 1977-09-06 Nasa Regenerable device for scrubbing breathable air of CO2 and moisture without special heat exchanger equipment
US4101691A (en) * 1976-09-09 1978-07-18 Union Carbide Corporation Enhanced heat transfer device manufacture
US4129181A (en) * 1977-02-16 1978-12-12 Uop Inc. Heat transfer surface
US4381818A (en) * 1977-12-19 1983-05-03 International Business Machines Corporation Porous film heat transfer
US4350025A (en) * 1980-04-18 1982-09-21 Nissan Motor Company, Limited Refrigerant evaporator
FR2486627A1 (en) * 1980-07-14 1982-01-15 Cryoplants Ltd HEAT EXCHANGER AND METHOD FOR BOILING LIQUIFIED GAS
US4353224A (en) * 1980-10-16 1982-10-12 Nippondenso Co., Ltd. Evaporator
EP0053452A3 (en) * 1980-12-02 1982-12-22 Imi Marston Limited Heat exchanger
EP0053452A2 (en) * 1980-12-02 1982-06-09 Marston Palmer Ltd. Heat exchanger
US4698135A (en) * 1983-02-10 1987-10-06 Sirdan Research Limited Desalinating drip-irrigation system
WO1986000124A1 (en) * 1984-06-14 1986-01-03 Total Energy Conservation & Management Company Lim Improvements in earth heat recovery systems
EP0236907A1 (en) * 1986-03-11 1987-09-16 Air Products And Chemicals, Inc. Heat exchanger for boiling liquids
EP0303492A2 (en) * 1987-08-14 1989-02-15 The BOC Group plc Liquefied gas boilers
EP0303492A3 (en) * 1987-08-14 1989-08-09 The BOC Group plc Liquefied gas boilers
US5014773A (en) * 1987-08-14 1991-05-14 The Boc Group Plc Liquefied gas boilers
US5752566A (en) * 1997-01-16 1998-05-19 Ford Motor Company High capacity condenser
US6082444A (en) * 1997-02-21 2000-07-04 Tocalo Co., Ltd. Heating tube for boilers and method of manufacturing the same
US5755113A (en) * 1997-07-03 1998-05-26 Ford Motor Company Heat exchanger with receiver dryer
US6186222B1 (en) * 1997-07-16 2001-02-13 The Furukawa Electric Co., Ltd Aluminum alloy tube and heat exchanger, and method of metal-spraying a filler alloy
EP1048918A2 (en) * 1999-04-28 2000-11-02 Haruo Uehara Evaporator
US6286588B1 (en) * 1999-04-28 2001-09-11 Haruo Uehara Evaporator
US6340052B1 (en) * 1999-04-28 2002-01-22 Haruo Uehara Heat exchanger
EP1048918A3 (en) * 1999-04-28 2002-03-27 Haruo Uehara Evaporator
US20020056546A1 (en) * 2000-02-02 2002-05-16 York International Corporation Plate heat exchanger assembly with enhanced heat transfer characteristics
US6666909B1 (en) * 2000-06-06 2003-12-23 Battelle Memorial Institute Microsystem capillary separations
US20050229553A1 (en) * 2000-06-06 2005-10-20 Tegrotenhuis Ward E Conditions for fluid separations in microchannels, capillary-driven fluid separations, and laminated devices capable of separating fluids
US7344576B2 (en) 2000-06-06 2008-03-18 Battelle Memorial Institute Conditions for fluid separations in microchannels, capillary-driven fluid separations, and laminated devices capable of separating fluids
EP1262725A3 (en) * 2001-05-22 2003-01-08 Praxair Technology, Inc. Cryogenic condensation and vaporization system
US7059130B2 (en) * 2002-02-13 2006-06-13 Ship & Ocean Foundation Heat exchanger applicable to fuel-reforming system and turbo-generator system
US20040103660A1 (en) * 2002-02-13 2004-06-03 Ship & Ocean Foundation Heat exchanger applicable to fuel-reforming system and turbo-generator system
US8579014B2 (en) * 2002-04-29 2013-11-12 Richard W. Kauppila Cooling arrangement for conveyors and other applications
US20100059205A1 (en) * 2002-04-29 2010-03-11 Kauppila Richard W Cooling arrangement for conveyors and other applications
US20060032242A1 (en) * 2003-01-27 2006-02-16 Tegrotenhuis Ward E Methods for fluid separations, and devices capable of separating fluids
US20070193284A1 (en) * 2003-01-27 2007-08-23 Tegrotenhuis Ward E Methods for fluid separations, and devices capable of separating fluids
US7272941B2 (en) * 2003-01-27 2007-09-25 Battelle Memorial Institute Methods for fluid separations, and devices capable of separating fluids
US7051540B2 (en) 2003-01-27 2006-05-30 Battelle Memorial Institute Methods for fluid separations, and devices capable of separating fluids
US7677300B2 (en) * 2003-05-30 2010-03-16 Uop Llc Method for making brazed heat exchanger and apparatus
US20080041573A1 (en) * 2003-05-30 2008-02-21 Uop Llc Method for making brazed heat exchanger and apparatus
US20080230212A1 (en) * 2004-01-12 2008-09-25 Frederic Crayssac Fin for Heat Exchanger and Heat Exchanger Equipped with Such Fins
US20100313599A1 (en) * 2004-01-12 2010-12-16 L'air Liquide Societe Anonyme Pour L'etude Et L'exploitation Des Procedes Georges Claude Fin For Heat Exchanger And Heat Exchange Equipped With Such Fins
US20080099191A1 (en) * 2005-02-02 2008-05-01 Carrier Corporation Parallel Flow Heat Exchangers Incorporating Porous Inserts
US7926793B2 (en) 2005-09-16 2011-04-19 Battelle Memorial Institute Mixing in wicking structures and the use of enhanced mixing within wicks in microchannel devices
US7540475B2 (en) 2005-09-16 2009-06-02 Battelle Memorial Institute Mixing in wicking structures and the use of enhanced mixing within wicks in microchannel devices
US20090211735A1 (en) * 2005-09-16 2009-08-27 Battelle Memorial Institute Mixing in Wicking Structures and the Use of Enhanced Mixing Within Wicks in Microchannel Devices
US7360581B2 (en) 2005-11-07 2008-04-22 3M Innovative Properties Company Structured thermal transfer article
US20080148570A1 (en) * 2005-11-07 2008-06-26 3M Innovative Properties Company Structured thermal transfer article
US20070102070A1 (en) * 2005-11-07 2007-05-10 3M Innovative Properties Company Thermal transfer coating
US7695808B2 (en) 2005-11-07 2010-04-13 3M Innovative Properties Company Thermal transfer coating
US20070102140A1 (en) * 2005-11-07 2007-05-10 3M Innovative Properties Company Structured thermal transfer article
WO2007100297A1 (en) 2006-03-03 2007-09-07 Richard Furberg Porous layer
US9103607B2 (en) 2006-03-03 2015-08-11 Micro Delta T Ab Porous layer
US20080023179A1 (en) * 2006-07-27 2008-01-31 General Electric Company Heat transfer enhancing system and method for fabricating heat transfer device
US8356658B2 (en) * 2006-07-27 2013-01-22 General Electric Company Heat transfer enhancing system and method for fabricating heat transfer device
WO2008078211A1 (en) * 2006-12-20 2008-07-03 Turk Demir Dokum Fabrikalari Anonim Sirketi A heat exchanger
US20090321053A1 (en) * 2008-06-05 2009-12-31 Battelle Memorial Institute Enhanced Two Phase Flow in Heat Transfer Systems
US8596341B2 (en) 2008-06-05 2013-12-03 Battelle Memorial Institute Enhanced two phase flow in heat transfer systems
EP2291598A1 (en) * 2008-06-30 2011-03-09 Uop LLC Methods of manufacturing brazed aluminum heat exchangers
EP2291598A4 (en) * 2008-06-30 2014-12-24 Uop Llc Methods of manufacturing brazed aluminum heat exchangers
WO2011154879A3 (en) * 2010-06-08 2012-03-15 Memc Electronic Materials, Inc. Trichlorosilane vaporization system
CN103025656A (en) * 2010-06-08 2013-04-03 Memc电子材料有限公司 Trichlorosilane vaporization system
EP2580159A4 (en) * 2010-06-08 2015-12-02 Memc Electronic Materials Trichlorosilane vaporization system
CN103025656B (en) * 2010-06-08 2016-02-10 Memc电子材料有限公司 Trichlorosilane vaporization system
US20130206368A1 (en) * 2010-10-19 2013-08-15 Nec Corporation Cooling device and method for producing the same
US20130048261A1 (en) * 2011-08-26 2013-02-28 Hs Marston Aerospace Ltd. Heat exhanger
US9279626B2 (en) * 2012-01-23 2016-03-08 Honeywell International Inc. Plate-fin heat exchanger with a porous blocker bar
US20150292818A1 (en) * 2012-08-18 2015-10-15 Audi Ag Heat exchanger
US9664459B2 (en) * 2012-08-18 2017-05-30 Audi Ag Heat exchanger with a porous metal structure having manifolds and tubes
US20170276434A1 (en) * 2014-08-29 2017-09-28 Kyungdong Navien Co., Ltd. Air guide-integrated evaporation cooler and method for manufacturing same
US10215498B2 (en) * 2014-08-29 2019-02-26 Kyungdong Navien Co., Ltd. Air guide-integrated evaporation cooler and method for manufacturing same
US20160377350A1 (en) * 2015-06-29 2016-12-29 Honeywell International Inc. Optimized plate fin heat exchanger for improved compliance to improve thermal life
US10047880B2 (en) 2015-10-15 2018-08-14 Praxair Technology, Inc. Porous coatings
US10221970B2 (en) 2015-10-15 2019-03-05 Praxair Technology, Inc. Air separation unit heat exchanger with porous boiling surface coatings
US10520265B2 (en) 2015-10-15 2019-12-31 Praxair Technology, Inc. Method for applying a slurry coating onto a surface of an inner diameter of a conduit
US10048024B1 (en) 2017-04-26 2018-08-14 Joshua D. Sole Two-phase fluid flow distributor and method for parallel microchannel evaporators and condensers

Similar Documents

Publication Publication Date Title
US3587730A (en) Heat exchange system with porous boiling layer
US3384154A (en) Heat exchange system
US3523577A (en) Heat exchange system
Rashidi et al. Potentials of porous materials for energy management in heat exchangers–A comprehensive review
US4998580A (en) Condenser with small hydraulic diameter flow path
Rudy et al. An analytical model to predict condensate retention on horizontal integral-fin tubes
US3537514A (en) Heat pipe for low thermal conductivity working fluids
EP0219974B1 (en) Condenser with small hydraulic diameter flow path
US3528494A (en) Heat pipe for low thermal conductivity working fluids
JP2008522129A (en) Steam chamber with boil-enhancing multi-wick structure
US3750745A (en) High heat flux heat pipe
US4353415A (en) Heat pipes and thermal siphons
US4216819A (en) Enhanced condensation heat transfer device and method
JPH0454879B2 (en)
CN100478639C (en) Fin for heat exchanger and heat exchanger equipped with such fins
US4154294A (en) Enhanced condensation heat transfer device and method
US3196634A (en) Refrigeration system
Li Design and preliminary experiments of a novel heat pipe using a spiral coil as capillary wick
Ma et al. Effects of geometrical shapes and parameters of reentrant grooves on nucleate pool boiling heat transfer from porous surfaces
US4232728A (en) Method for enhanced heat transfer
EP0145867A2 (en) Ultra-low fin heat exchanger with enhanced heat transfer
Kuznetsov et al. Experimental investigation of heat transfer at downflow condensation of refrigerant R-21 in assemblage of minichannels
IL31978A (en) Process for transferring heat from heated surfaces to boiling liquids
WO1992015833A1 (en) Condenser with small hydraulic diameter flow path
RU2699116C2 (en) Metal thermal heat flow pipe

Legal Events

Date Code Title Description
AS Assignment

Owner name: MORGAN GUARANTY TRUST COMPANY OF NEW YORK, AND MOR

Free format text: MORTGAGE;ASSIGNORS:UNION CARBIDE CORPORATION, A CORP.,;STP CORPORATION, A CORP. OF DE.,;UNION CARBIDE AGRICULTURAL PRODUCTS CO., INC., A CORP. OF PA.,;AND OTHERS;REEL/FRAME:004547/0001

Effective date: 19860106

AS Assignment

Owner name: UNION CARBIDE CORPORATION,

Free format text: RELEASED BY SECURED PARTY;ASSIGNOR:MORGAN BANK (DELAWARE) AS COLLATERAL AGENT;REEL/FRAME:004665/0131

Effective date: 19860925