CA2025074C - Versatile, overpressure proof, absolute pressure sensor - Google Patents
Versatile, overpressure proof, absolute pressure sensor Download PDFInfo
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- CA2025074C CA2025074C CA002025074A CA2025074A CA2025074C CA 2025074 C CA2025074 C CA 2025074C CA 002025074 A CA002025074 A CA 002025074A CA 2025074 A CA2025074 A CA 2025074A CA 2025074 C CA2025074 C CA 2025074C
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- G—PHYSICS
- G01—MEASURING; TESTING
- G01L—MEASURING FORCE, STRESS, TORQUE, WORK, MECHANICAL POWER, MECHANICAL EFFICIENCY, OR FLUID PRESSURE
- G01L11/00—Measuring steady or quasi-steady pressure of a fluid or a fluent solid material by means not provided for in group G01L7/00 or G01L9/00
- G01L11/002—Measuring steady or quasi-steady pressure of a fluid or a fluent solid material by means not provided for in group G01L7/00 or G01L9/00 by thermal means, e.g. hypsometer
Abstract
A non membrane-based overpressure proof gas pressure microsensor. Since it is not a membrane-based microsensor but is based on an open microbridge sensor structure (Fig. 8); it is not subject to breakage caused by overpressure. A method is described to determine gas pressure from thermal conductivity, k, and volumetric specific heat, C pv.
Description
2025~~~
PATENT
VERSATILE, OVERPRESSURE PROOF, ABSOLUTE
PRESSURE SENSOR
BACKGROUND OF THE INVENTION
1. Field of the Invention The present invention relates to a non membrane-based gas pressure microsensor. It is based on the microbridge flow sensor and since it is not membrane-based it is not subject to breakage caused by overpressure. It describes a method to determine gas pressure from basically thermal conductivity, k, and specific heat, cpv.
PATENT
VERSATILE, OVERPRESSURE PROOF, ABSOLUTE
PRESSURE SENSOR
BACKGROUND OF THE INVENTION
1. Field of the Invention The present invention relates to a non membrane-based gas pressure microsensor. It is based on the microbridge flow sensor and since it is not membrane-based it is not subject to breakage caused by overpressure. It describes a method to determine gas pressure from basically thermal conductivity, k, and specific heat, cpv.
2. Background Prior art gas pressure microsensors are typically based on sensing the deflection of a membrane either piezoresistively or capacitatively, with inherent limitations imposed by allowable maximum pressure to avoid membrane breakage and by acceptable sensitivity at the low pressure end. Over-pressure protection is needed and costly. A non membrane-based absolute pressure microsensor is based on sensing thermal conductivity, but has a limited high pressure range and has a somewhat gas composition dependent output.
SUMMARY OF THE INVENTION
The present invention presents a new "high accuracy", wide range, absolute or differential pressure ~Q2~~~
microsensor, based on a microbridge sensor, in a situation where the gas composition is known. The present invention also presents a "medium accuracy"
(max error <+ 0.1%), wide range, absolute or differential pressure microsensor if the gas composition is only approximately known or is not known. This microsensor is not membrane-based and therefore is not subject to breakage through overpressure. Thermal conductivity, k, and specific heat, cpv, can be measured with the microbridge and herein a method is shown to determine gas pressure from k and cpv.
BRIEF DESCRIPTION OF THE DRAWINGS
Figures 1, 2, and 3 are different views of a prior art embodiment of a microbridge sensor, used to sense flow and Figures 4-18 are supporting figures.
Figures 4 and 5 are typical circuits for use with the sensors of Figures 1-3.
Figure 6 is a schematic representation of sensor time/temperature response curves caused by an electric pulse to a film heater element.
Figures 7a, 7b, and 7c, represent several heater/sensor configurations of microbridge systems in accordance with the invention.
Figure 8 is a scanning-electron-microscope (SEM) photo of the microstructure of a typical microbridge sensor.
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Figure 9 is a partial schematic and block diagram of a circuit for use with a sensor as depicted in Figure 7(b) in accordance with the invention.
Figure 9a is a more detailed circuit schematic with reference to Figure 7c.
Figure 10 is a schematic block diagram of the system of the invention including calibration and use functions.
Figure 11 is a scope trace representing the temperature signal rise versus time, for the configuration of Figure 7(c) in response to a heater a pulse to the heater of a microbridge located in dry air at atmospheric pressure.
Figure 12 is a graphical representation of the temperature signal rise versus time, for the configuration of Figure 7(c) in response to the heater pulse for various gases at atmospheric pressure as indicated.
Figure 13 is a graphical representation of thermal conductivity determination based on the bridge output of Figure 9(a).
Figure 14 is a theoretical graphical representation of sensor heat-up time versus pressure for several gases using the sensor configuration of Figure 7b.
SUMMARY OF THE INVENTION
The present invention presents a new "high accuracy", wide range, absolute or differential pressure ~Q2~~~
microsensor, based on a microbridge sensor, in a situation where the gas composition is known. The present invention also presents a "medium accuracy"
(max error <+ 0.1%), wide range, absolute or differential pressure microsensor if the gas composition is only approximately known or is not known. This microsensor is not membrane-based and therefore is not subject to breakage through overpressure. Thermal conductivity, k, and specific heat, cpv, can be measured with the microbridge and herein a method is shown to determine gas pressure from k and cpv.
BRIEF DESCRIPTION OF THE DRAWINGS
Figures 1, 2, and 3 are different views of a prior art embodiment of a microbridge sensor, used to sense flow and Figures 4-18 are supporting figures.
Figures 4 and 5 are typical circuits for use with the sensors of Figures 1-3.
Figure 6 is a schematic representation of sensor time/temperature response curves caused by an electric pulse to a film heater element.
Figures 7a, 7b, and 7c, represent several heater/sensor configurations of microbridge systems in accordance with the invention.
Figure 8 is a scanning-electron-microscope (SEM) photo of the microstructure of a typical microbridge sensor.
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Figure 9 is a partial schematic and block diagram of a circuit for use with a sensor as depicted in Figure 7(b) in accordance with the invention.
Figure 9a is a more detailed circuit schematic with reference to Figure 7c.
Figure 10 is a schematic block diagram of the system of the invention including calibration and use functions.
Figure 11 is a scope trace representing the temperature signal rise versus time, for the configuration of Figure 7(c) in response to a heater a pulse to the heater of a microbridge located in dry air at atmospheric pressure.
Figure 12 is a graphical representation of the temperature signal rise versus time, for the configuration of Figure 7(c) in response to the heater pulse for various gases at atmospheric pressure as indicated.
Figure 13 is a graphical representation of thermal conductivity determination based on the bridge output of Figure 9(a).
Figure 14 is a theoretical graphical representation of sensor heat-up time versus pressure for several gases using the sensor configuration of Figure 7b.
20~~~~4 Figure 15 is similar to Figure 14 based on data taken by a sensor of the type depicted in Figure 7(b) calculated in accordance with the invention.
Figure 16 is a graphical representation of sensor heat-up time versus pressure for several gases using the sensor configuration of Figure 7c.
Figure 17 is a graphical representation of sensor cooling time versus pressure for several gases using the sensor configuration of Figure 7c.
Figure 18 is a graphical presentation of the heat-up time versus pressure and gas type according to the invention.
Figure 19 is a graphical presentation of the specific heat of several gases versus thermal conductivity.
Figure 20 is a graphical presentation showing a determination of pressure from the output of a standard microbridge sensor, used to sense cp, kc and kh.
Figure 21 is a graphical presentation of gas pressure versus thermal conductivity for 78 natural gases and several gas temperatures. (~ B 15°C
higher) ks and cps at 1 atm and 15.6°C.
Figure 22 is a graphical presentation of gas pressure versus thermal conductivity for 78 natural gases and several gas temperatures (u B 15°C
higher) ks and cps at 1 atm and - 12.2°C.
k ~o~~a~;~
Figure 23 is a graphical presentation of gas pressure versus thermal conductivity for 78 natural gases and several gas temperatures. (~c B 15°C
higher) ks and cps at 1 atm and 15.6°C with iteration.
Figure 24 is a graphical presentation of specific heat versus thermal conductivity at several pressures (1, 2, 4 and 8 atm).
DETAILED DESCRIPTION
This invention is directed to a non membrane-based, overpressure-proof, absolute pressure sensor of the microbridge sensor type. The principle on which this pressure sensor operates includes that of sensing specific heat, cp, with a pulsed microbridge heater, as is taught in the co-pending applications Serial No. 210,892, filed June 24, 1988, entitled "Measurement of Thermal Conductivity and Specific Heat", and Serial No. 211,200, filed June 24, 1988, entitled "Calibration of Thermal Conductivity and Specific Heat Devices", both co-pending applications being assigned to the same assignee as the present application, which principle shows that the signal generated by a sensor next to the heater is related to volumetric specific heat, cpv, for example, in units of cal/(cm3C). The sensor output is pressure dependent and is composition dependent.
Figure 16 is a graphical representation of sensor heat-up time versus pressure for several gases using the sensor configuration of Figure 7c.
Figure 17 is a graphical representation of sensor cooling time versus pressure for several gases using the sensor configuration of Figure 7c.
Figure 18 is a graphical presentation of the heat-up time versus pressure and gas type according to the invention.
Figure 19 is a graphical presentation of the specific heat of several gases versus thermal conductivity.
Figure 20 is a graphical presentation showing a determination of pressure from the output of a standard microbridge sensor, used to sense cp, kc and kh.
Figure 21 is a graphical presentation of gas pressure versus thermal conductivity for 78 natural gases and several gas temperatures. (~ B 15°C
higher) ks and cps at 1 atm and 15.6°C.
Figure 22 is a graphical presentation of gas pressure versus thermal conductivity for 78 natural gases and several gas temperatures (u B 15°C
higher) ks and cps at 1 atm and - 12.2°C.
k ~o~~a~;~
Figure 23 is a graphical presentation of gas pressure versus thermal conductivity for 78 natural gases and several gas temperatures. (~c B 15°C
higher) ks and cps at 1 atm and 15.6°C with iteration.
Figure 24 is a graphical presentation of specific heat versus thermal conductivity at several pressures (1, 2, 4 and 8 atm).
DETAILED DESCRIPTION
This invention is directed to a non membrane-based, overpressure-proof, absolute pressure sensor of the microbridge sensor type. The principle on which this pressure sensor operates includes that of sensing specific heat, cp, with a pulsed microbridge heater, as is taught in the co-pending applications Serial No. 210,892, filed June 24, 1988, entitled "Measurement of Thermal Conductivity and Specific Heat", and Serial No. 211,200, filed June 24, 1988, entitled "Calibration of Thermal Conductivity and Specific Heat Devices", both co-pending applications being assigned to the same assignee as the present application, which principle shows that the signal generated by a sensor next to the heater is related to volumetric specific heat, cpv, for example, in units of cal/(cm3C). The sensor output is pressure dependent and is composition dependent.
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The relation between molar (or weight)-based specific heat, cp, and volumetric specific heat, cpv, leads to the ability to determine pressure, P, according to the relation:
cp - Cpv VMo (T/To) (Po/P) where cp - specific heat, (molar or weight)-based cpv - volumetric specific heat VMo - molar volume of ideal gases = 22415 cm3/mol @
273.15° and 760mm Mercury of pressure T - sensed gas temperature in °K
To - gas temperature at the reference condition of 273.15 °K
Po - gas pressure at the reference condition of 760mm Mercury P - actual gas pressure of the sensor In the equation above everything is known (cp) or sensed (T
and cpv) if the gas composition is known, so that P can be computed. Referring to Figure 19, which graphically shows specific heat, cp, in cal/(mol °K) versus thermal conductivity, k, in ~c cal/ (s°Ccm) or in Btu/(s F ft), Figure 19 shows that for most gases used in fuels, there is a clear relation among the family of hydrocarbons, i.e. cp and 1/k increase as molecular weight increases. This relation only approximately extends to N2, 02 and C02 which also are part of such fuel gases, although mostly in low concentrations (exceptions:
peak shaving gas and town or city gas, with sizeable amounts of CO, H2, N2 and C02.
The relation between molar (or weight)-based specific heat, cp, and volumetric specific heat, cpv, leads to the ability to determine pressure, P, according to the relation:
cp - Cpv VMo (T/To) (Po/P) where cp - specific heat, (molar or weight)-based cpv - volumetric specific heat VMo - molar volume of ideal gases = 22415 cm3/mol @
273.15° and 760mm Mercury of pressure T - sensed gas temperature in °K
To - gas temperature at the reference condition of 273.15 °K
Po - gas pressure at the reference condition of 760mm Mercury P - actual gas pressure of the sensor In the equation above everything is known (cp) or sensed (T
and cpv) if the gas composition is known, so that P can be computed. Referring to Figure 19, which graphically shows specific heat, cp, in cal/(mol °K) versus thermal conductivity, k, in ~c cal/ (s°Ccm) or in Btu/(s F ft), Figure 19 shows that for most gases used in fuels, there is a clear relation among the family of hydrocarbons, i.e. cp and 1/k increase as molecular weight increases. This relation only approximately extends to N2, 02 and C02 which also are part of such fuel gases, although mostly in low concentrations (exceptions:
peak shaving gas and town or city gas, with sizeable amounts of CO, H2, N2 and C02.
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The idea to be further discussed below is based on taking a small segment of Figure 19, corresponding to the range of composition of natural gases, leading to average cp and k values near to those of methane, and to prove that even without knowing the exact composition within the chosen gas composition range, a meaningful determination of pressure, P, can be made.
Such a determination of P is needed for gas flow controls, combustion controls, and flow sensing devices (like gas meters) in order to eliminate the composition effect on the signal output of hot thin film (anemometer type) flow sensors; the use of regular pressure sensors would be too costly for such applications.
Several embodiments of this invention to obtain pressure have been conceived. Figure 20 shows an early version in which the sensed cpv in cal/(cm3C), kh and kc are combined to compute P, for gases covering a wide range: 78 natural gases and 77 peak shaving gases (50%
natural gas + 25% air + 25~ propane). No attempt was made in this embodiment to increase the accuracy by also using measurable cpv at more than one temperature. Note that the output of one sensor, cpv, is pressure sensitive, while that of the other one is not (or very little:
2.5~/atm near 1 atm); this is an important part of this pressure sensing method, which works without knowing the exact composition of the gas.
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Figure 21 which plots pressure, P, versus thermal conductivity, k, at various temperatures, shows the result of a more accurate method, although it requires more involved computations, to be discussed next.
First as is shown in co-pending application, Serial No. filed , Table 1 shows the result of deriving a number of algorithms to compute ks and cps, i.e., the properties at reference conditions of temperature, TS (and Ps), which were chosen as 60F (15.555°C) and 14.73 psia (1 atm). The actual computations were made for 15°C higher to allow for the influence of the microbridge heater on raising the average gas temperature around it. A set of over 60 natural gases used to derive these algorithms were chosen to represent a range of typical natural gases. They contain less than 2$ each of N2 or C02, no more than 0.1% 02, and no less than 85~ CH4. The chosen temperature range is from -12.2 to 45.6°C (10 to 114F).
The standard errors of the investigated algorithms vary from 5000 ppm (0.5%) down to 153 ppm, with maximum errors about 3 to 4x larger. For clarity sake the exponents of the listed polynomials have been omitted, although all are of the general form:
1/ks or 1/cps or ks or cps=A+BTb+Ckc+Dcpd+E(kTx)e+F(cpTy)f+G(dk/dT)g+H(dcp/dT)h(1) _g_ .h.
with one or more of the terms missing in order to simplify the expressions as much as possible.
The algorithms listed in Table 1 (an abbreviated Table) are preferred because the equations 3 and 4 achieved the lowest error, while equations 2 and 5 are preferred because they achieved a reasonably low error without requiring measurements at more than one microbridge heater temperature (low cost compromise).
The choices which were considered in converting the measured k and cp from the measurement* to the reference temperature (60°F, 15.555°C) values ks and cps are expressed in terms of the following functional relationships:
Table 1 CONVERSION OF k AND cp TO REFERENCE TEMPERATURE
Errors Std. Max. Log.
PPM PPM Sens.
ks - A BT + Ck + D(kT) 287 1931 2.00 +
ks - A BT + Ck + D(dk/dT) 153 +
1/cps A BT + Ccp + Ddcp/dT 165 = +
c A BT + C(c + D(kT) 197 660 1.51 - + /T) ps p The coefficients and exponents for these four preferred algorithms are as follows, with all k-values in microcal/(s°Ccm), cp in cal/(mol°C), T in °K:
t 2(~~~~'~~
Table 2 R~i.
~i.0?iLLY.~ .~ ..~ .~ ..~. ...p...
cLl ks 51.3ldb!-.005=31d1!l.dl3t1! 1.101961.ldl0=173-.l7 I1 l1! 10-s Z
1.110100 k s 61.117!.old~lss 1.1d0'3 1.5120 .91511 -lt~!)I 11.317 l c') cQ 51.7511!Id.ts111 .07dsss0! -1361.191-1.100177I.OId4~107 1.10711!
s cL) cp 1.SZ=11!-17iZ17.1 -3.01471 Sld.7ls1.1)!!1 3.19!S~Ols -;,t;1t315 s cp/eD .07113ds1~ .916741!(()~k)/tTa/T)x)-1.6661d~
s =~(Z/Za)0.3 Eq. (6) above was also discovered during this study and is listed here as an additional, very useful relation.
As shown, the top two algorithms only involve inputs of thermal conductivity properties, while the bottom one was both k and cp inputs to compute cps.
Secondly, the basis for the more accurate method mentioned above are the two algorithms eqs. (5) and (6), which compute cps and cp/cps, respectively: forming also cp/cps in the former and equating it to the latter, eliminates cps. Then, substituting the remaining cp by eq. (1) we obtain an equation for P:
P = cpv T Po VMo/To(f(k~T)9(k.T)) (7) where 260 <T <310K, Po = 1 atm, To = 273.15°K, VMS=22415(T/To)(Po/P) cm3/mol, f(k,T) and g(k,T) are i ~02~0~~
the right hand sides of eqs. (5) and (6), respectively, note that f(k,T) also contains a term with cp (see eq.
(1)) and therefore with Pc with c=1 listed in eq. (5) mentioned above, an iteration of the solution of P is needed. Results obtained with eq. (2) are as follows:
Figure 21 shows a plot of 78 natural gases at 5 temperatures and three pressures, whereby actual values of k, ks, T and TS were used to compute cp/cps with eq. (6); these were then converted to cpv/cpvs ratios via eq. (1) for three pressures and compared (i.e. ratioed) to actual values of cp/cps. The match between the points P=(cpv/cpvs)/(cp.cps) and the lines drawn for constant pressure of 0.9, 1.09 and 1.1 atm gives an indication of the accuracy of eq. (6): std. error of +254 ppm and max. error of 1077 ppm. Figure 22 shows that sizeable errors result if the incorrect reference temperature is used (-12.2.°C rather than 15.6°C).
Figure 23 presents a blown up version of the center part of Figure 19 in order to visualize the error margin achieved by the computation: note that the maximum error, obtained with half of the natural gases not used for the derivation of the equations is still within +1500 ppm.
Figure 23 presents a plot of the same gases, but now simulating a more comprehensive test of eq. (2): its solution was iterated to a value of P to within + 10 ppm by i 2~2~~'~~~
using the outputs of f(k,T) and g(k,T) from "sensed" k and T, and computing ks from eq. (8) ks = A + B Tb + Ckc + D ( kT ) d ( 8 ) which was derived earlier as eq. (2); the "sensed" value of cpv is obtained experimentally via a method described in copending applications SN 210,892 filed June 24, 1988 and SN 211,200 filed June 24, 1988 and assigned to the same assignee as the present application.
The System Thus the ability to measure pressure with a non membrane-based microbridge sensor has been shown above. In order to more fully appreciate the microbridge flow sensor system upon which the present method invention is utilized to extend the applicability thereof, the following description is supplied.
Thermal conductivity and specific heat of each fluid of interest produce characteristic transient and steady-state temperature reactions in a proximate sensor as exemplified in Figure 6.
In the preferred implementation, specific temperatures, as T1 and T2 in Figure 6, are selected as "marker" points with respect to the sensor. These marker points are used to reference the determination of the time periods, as t1 - t2, required to achieve the corresponding temperature rises) or falls) in the sensors) between the marker points. As will be discussed, the sensor or sensors are located in predetermined spaced t 202~0~~
relation to the heater or heaters, but preferably.
physically separated therefrom so that the proximate influence of the solid heater materials) is reduced and the coupling of the heater with the sensor or sensors by the fluid of interest is relatively enhanced.
The preferred embodiments of the approach of the invention contemplate disposing spaced microspec sized heating and sensing elements in a relatively static (zero flow) sample of the fluid of interest. The microsensor system or "microbridge" system, as it will be referred to herein, though not limiting, is presently preferred for several reasons. The system is extremely fast reacting, is very accurate, very sensitive because of its advantageous coupling to the fluid of interest and small and adaptable to a variety of configurations.
The microbridge chip sensor contemplated, for example, in certain embodiments preferred for the invention may resemble the form of one or more of the microbridge systems illustrated in the patents identified above. Such a system is exemplified by Figures 1-5 taken from Patent 4,501,144. A discussion of that example will now be presented as it will be helpful in understanding the present invention. While the present discussion is believed sufficient, to the extent necessary, any additional material contained in the microbridge related patents cited is deemed to be incorporated herein by reference.
t 2~~~~~~
The illustrated embodiment of Figures 1-5 contemplates a pair of thin film temperature sensors 22 and 24, a thin film heater 26 and a base 20 supporting the sensors and heater out of contact with the base.
Sensors 22 and 24 are disposed on opposite sides of heater 26. Body 20 is a semiconductor, preferably silicon, chosen because of its adaptability to precision etching techniques and ease of electronic chip producibility. The embodiment includes two identical temperature sensing resistor grids 22 and 24 acting as the thin film heat sensors and a centrally located heater resistor grid 26 acting as the thin film heater.
Sensors 22 and 24 and heater 26 may be fabricated of any suitable, stable metal or alloy film.
In Figure 8, the metal used was a nickel-iron alloy sometimes referred to as permalloy, with a composition of 80 percent nickel and 20 percent iron. The sensor and heater grids are encapsulated in a thin film of dielectric, typically comprising layers 28 and 29 and preferably silicon nitride, Si3N4, to form thin film members. In the embodiment shown in Figures 1 and 2, the sensor comprises two thin film members 32 and 34, member 32 comprising sensor 22 and 34 comprising sensor 24, each member comprising one-half of heater 26 and having a preferred dimension of 150 microns wide and 400 microns long.
t The embodiment of the system further describes an accurately defined air space 30 which contemplates air space effectively surrounding elements 22, 24, 26.
The effectively surrounding air space is achieved by fabricating the structure on silicon surface 36, thin film elements 22, 24 and 26 having a preferred thickness of approximately 0.08 to 0.12 micron with lines on the order of 5 microns wide and spaces between lines on the order of 5 microns, the elements encapsulated in a thin silicon nitride film preferably having a total thickness of approximately 0.8 microns or less, and by subsequently etching an accurately defined air space, of about 100 microns deep, into silicon body 20 beneath members 32 and 34.
Members 32 and 34 connect to top surface 36 of semiconductor body 20 at one or more edges of depression or air space 30. As illustrated in Figure 3, members 32 and 34 may be bridged across depression 30~ alternately, for example, members 32 and 34 could be cantilevered over depression 30.
Heat flows from the heater to the sensor by means of both solid and fluid couplings there between.
Of note is the fact that silicon nitride (Si3N4) is a highly effective solid thermal insulator. Because the connecting silicon nitride film within members 32 and 34 is a good insulator, heat transmission through the solid does not dominate the propagation of heat from heater f 26. This further enhances the relative amount of the heat conducted to sensing resistor 22 and 24 from heater resistor 26 by flow through the surrounding fluid rather than through the supporting nitride film. Moreover, the supporting silicon nitride film has a low enough thermal conductivity that sensing resistor grids 22 and 24 can be located immediately adjacent or juxtaposed to heating resistor grid 26. Thus, sensing resistor grids 22 and 24 are in effect suspended rigidly in the air space proximate heater resistor 26 and act as thermal probes to measure the temperature of the air near and in the plane of heater resistor grid 26.
The operation of the system in sensing air flow is described in detail in the above-referenced U.S.
patent 4,501,144. Typical circuit implementation is discussed briefly with reference to Figures 4 and 5 to add some insight. The heater control circuit illustrated in Figure 4 uses a Wheatstone bridge 46 which further typically includes heater resistor 26 and a resistor 40 in its first leg and a resistor 42, heat sink resistor 38, and a resistor 44 in its second leg.
An error integrator includes amplifiers 48 and 50 keeps bridge 46 balanced by varying the potential across it and thus the power dissipated in heater resistors 26.
The circuitry of Figure 5 monitors the resistance difference between downstream sensor 24 and upstream sensor 22. This circuitry includes a constant r ~Q~~~~
current source 52 comprising an amplifier 72 and a differential amplifier 54 further including amplifiers 68 and 70. The constant current source drives a Wheatstone bridge comprising two high impedance resistors 56 and 58 in one leg and the two sensing resistors 22 and 24 with a hulling potentiometer 60 in the other leg. The gain of differential amplifier 54 is adjusted by potentiometer 62. Output 64 provides an output voltage that is proportional to the resistance difference between the two sensing resistors 22 and 24.
To get some concept of the small size of the microbridge, the power required by heater resistor to heat such a device 200°C, for example, above ambient temperature is less than 0.010 watt. The exceedingly small thermal mass of the heater and sensor element structures, their excellent coupling to the surrounding fluid because of a high surface/volume ratio, and the thermal insulation provided by the thin silicon nitride connecting them to the supporting silicon body, and the surrounding air space, all contribute to produce a system well suited to fast and accurate sensing.
Response time constants as short as 0.005 second have been measured. Consequently, sensor elements can respond very rapidly to proximate environmental changes.
Now with reference to the implementation of the present invention, Figures 7a, 7b, and 7c, depict three slightly differing embodiments or configurations which 2~!?~~'~~.
were taught in copending applications SN 210,892 and SN 211,200 mentioned above, and are representative in terms of number and arrangement of the heaters and sensors which can be used in implementing this invention. In Figure 7a, in contrast to Figure 1, all of the elements 122, 124 and 126 are used as heaters.
Figure 7b is an embodiment which is similar to the embodiment of Figure 1 with thin film element 126 acting as heater and elements 122 and 124 acting as sensors.
The embodiment of Figure 7c, represents the preferred arrangement in which the element 122 acts as heater and element 124 acts as sensor. The effective gap and thus the thermal isolation between heater and sensor is desirably wider in the embodiment of Figure 7c.
The actual general geometric structure of the embodiments of Figures 1-3, and 7a-7c is more clearly illustrated in the scanning electron micrograph (SEM) photo of Figure 8. The precision with which the cavity and bridge elements are defined and located in spaced relation, as Figure 8 depicts, is particularly noteworthy. The SEM represents a magnification such that the indicated length of 0.010" appears as shown.
In the implementation of the invention disclosed herein particular attention is directed to (1) setting specific temperature markers in the sensor to determine the time periods needed for achieving the corresponding temperature changes, (2) using temperature 2G~~~"~
sensors which are physically separated from the heater so that the direct influence of the heater and heat conducted to the sensor other than via the fluid of interest is reduced, and (3) using a pulse which reaches at least a momentary steady-state plateau to determine k, which then is used with the transient measure to determine cp.
Figure 6 graphically depicts a square wave electrical energy pulse 130 to the heater as at 126 which results in quasi square wave heat pulses released by the heater. These in turn, result in reactive curves as at 131, 132 and 133 at the sensor which vary as described below. The pulse applied to the heater, for example, may have a height of about 4 volts with a pulse width of 100 ms. Since the heater is closely coupled through the fluid medium to the sensors, the family of curves 131, 132 and 133 resembles the shape of the input pulse 130. They show the heat response in the sensors 122 and 124. Figure 11 represents an oscilloscope trace showing temperature rise and fall versus time for dry air at atmospheric pressure. It uses a different scale for time than does Figure 6, but illustrates the curve form produced by the pulsed input. The curves generally include beginning and ending transient portions flanking a relatively steady-state central portion. The relatively quick response of the sensor allows a relatively long steady-state to exist even with a pulse t ~~a0~!
of 100 ms. Of course, the curves are affected by factors such as pressure and temperature as they influence the effective thermal conductivity and specific heat of the particular fluid of interest.
Heat flowing from the heater element or elements to the sensor element or elements is conducted both through the fluid and through the solid semiconductor element support substrate or the like. It is advantageous with respect to the measurement of k or cp of the fluid of interest that the amount of heat reaching the sensor through the solid connections be minimized so that substantially all the measured thermal effect is generated via the fluid of interest.
With respect to the transfer of heat to the sensors) some background information regarding the propagation of heat or temperature waves is presented.
The speed of propagation, v, of a one dimensional wave (if it features an exponential decay profile) is constant and given by the expression:
v - DT~a = (DT~b) 0.5~ (9) where:
a is an exponential decay (length) constant b is the rise time constant at a fixed location and DT is the thermal diffusivity.
i 2~~~~~4 A complete list of nomenclature and subscripts with units appears in Table 3, below. DT is related to k and cp by the expression DT = k/cp (10) DT, therefore, if known, may be a key to obtaining cp. The rise time constant, b, was measured to be about 4 msec. For typical gases, DT ranges from 1.7 cm2/s for He to .054 cm2/s for C3H8. Metals exhibit high values such as 1.7, 1.1 and .18 cm2/s respectively for Ag, Cu and Fe. Insulators, however, are even lower than the gases at .004 cm2/s for glass and .0068 cm2 for Si3N4 which, as discussed above, is a good insulator. The propagation speed, v, in a typical gas sample then is about (1/0.004)0'5 = 15 cm/s. This compares with (0.0068/0.004)0'5 = 1.3 cm/s for Si3N4, assuming that the same rise time constant of about 4 ms is applicable to both the one measured in the Si3N4 and the actual one in the gas.
The effect is that the influence of the temperature wave propagating from one thin film strip, that is, the heater, to a second thin film strip, the sensor, both being embedded in a membrane of Si3N4, is faster for the gas than for the Si3N4. This also supports the choice of a material such as Si3N4, since it reduces the contribution of heat flow through the solid media. This is beneficial to the accuracy of the system.
i 2~~~0'~~
Typical microbridge embodiments are illustrated by Figures 7a - 7c. They will now be explained in greater detail.
Symbol Units Exponential Decay Constant cm al-anConstant A Area of Heat Transfer to Microbridge cm2 or to Gas b Rise Time Constant at a Fixed Location C/s c Specific Heat cal/ (cm3C) p DT Thermal Diffusivity, DT = k/cp cm2/s k Thermal Conductivity cal/(smC) L Length of Thermal Conductance Path cm in Gas or Solid P Pressure of Gas psia Q Power of Heat Release Rate watts Ro Resistance at Room Temperature ohms t Time s T Absolute Temperature C
U Bridge Output or Amplified Bridge V
Output V Volume of Gas or Solid (Microbridge) cm3 v Speed of Propagation cm/s x Temperature coefficient of resistance C-1 SUBSCRIPTS
c Conduction S Microbridge or Solid g Gas o Room, Reference or Gas Temperature Without Microbridge Heating h Heater or Hot m Middle or Medium The configuration of Figure 7a involves using the same microresistance 122, 124, 126 for the heating pulse and the sensing task. In this embodiment of the resistive heater-sensor element may be one leg of a conventional resistive Wheatstone bridge in a control circuit.
Figure 7b depicts an arrangement wherein the center microresistance structure 126 is used as a heater flanked by two symmetrically located outer sensing resistance elements 122 and 124. The elements 122 and 124 are separated from the heater 126 by a narrow gap.
Figure 7(c) shows an embodiment configuration in which the left element of the bridge 122 is used as the heating element and the right element 124 as the sensor. This embodiment takes advantage of a rather large central gap to achieve improved thermal isolation between the heater and the sensor.
Figure 9 shows a modified control circuit which uses the center microresistance 126 as heater, while the sensing task is performed by the two resistors 122 and 124. The dual heater sensor configuration corresponds to Figure 7b and the circuit is representative of typical sensor/measurement circuit. Figure 9 includes a timer 140 providing square-wave electrical pulses to the heater 126. The heater couples the heat pulse to the sensors 122 and 124 in the bridge 142. The output of the bridge is connected through an amplifier 143 to a i 2~2~~~
pair of comparators 144 and 145 which operate "start"
and "stop" inputs to a counter 146 which counts 10 mHz clock pulses. The counter counts measure the time interval (t2 - tl) between temperatures T2 & T1 illustrated in Figure 6.
Figure 9a is similar to Figure 9, but more detailed. The bridge configuration is the heater -space-sensor configuration of Figure 7c. The sensor resistance arm of the microbridge is set into a Wheatstone bridge 150 at 124. Another proximate resistive arm 122 is fed a voltage pulse from pulse generator 151 to provide a heat pulse into the microbridge element 126. The Wheatstone bridge 150 also may contain a nulling balancing resistor 152 which can be used in the manner of potentiometer 60 in Figure 5 to initially zero the device. The microbridge resistor sensor 124 in the Wheatstone bridge receives the heat pulse from heater element 122 principally by thermal conduction through the surrounding fluid. Some conduction, of course, does occur through the solid microbridge substrate and surroundings.
The circuitry of Figure 9a is conventional and can readily be explained with reference to its functional operation with regard to processing the bridge output signal. The voltage output signals of the bridge 150 are amplified by differential amplifiers 153 and 154 in a differential amplifier section. The t ~~?~~'~4 imbalance signal is further amplified by a high gain amplifier at 155. The signal at 156 as is the case with the signal at 147 in Figure 9 is in the form of a DC
voltage signal, U, the amplitude of which is solely related to the thermal conductivity of the fluid of interest as will be discussed above.
The remainder of the circuitry of Figure 9a includes a DC level clamping amplifier 157 and isolation amplifier 158. The temperature level, time-related switching and counting circuitry includes comparators 159 and 160 together with Nand gates 161 and 162 having outputs which are connected to the counter timing device (not shown) as in Figure 9. By measuring the time needed for the sensor temperature to rise or fall between two or more known temperature values or markers as represented by sensor resistance or bridge voltage outputs a measure related to the specific heat per unit volume, cp of the fluid of interest is obtained. The timing device may be a conventional 10 MHz pulse counter or the like. Again, this is illustrated schematically in Figure 6.
The output signal from the Wheatstone bridge, U, represents the voltage imbalance caused by the temperature change in microbridge sensor or sensors induced by the corresponding heater pulse output.
Because the magnitude of this imbalance is related directly to the amount of energy absorbed by the sensor i 2~~~~'~~
or sensors, the amplitude of the signal is directly related to the thermal conductivity, k, of the conducting media in a manner next explained.
Figure 6 shows that during much of the about 100ms wide pulse period the temperature of the sensor reaches and maintains a constant value. During this time, the influence of the energy sink or source terms represented by specific heat are zero, which means that only thermal conductivity governs the value of the sensor temperature.
Figure 12 is a plot of temperature rise in the form of bridge output, U, (Figure 9 or 9a) using the sensing arrangement of Figure 7(b) versus time in milliseconds for various gases at atmospheric pressure.
Curves for methane, dry air, ethane and a vacuum are presented. In this specific embodiment there was a heater resistance of 800 ohms, a pulse height of 2.5 volts, and a pulse width of 100 ms. Temperature markers t, and t2 are shown on the graph. These markers relate to those of Figure 13 which shows a graphical presentation of heat up time versus pressure for several gases with a sensor-heater such as that shown in Figure 7b and using the T2-T1, marked in Figure 11.
The literature value of the thermal conductivity of several gases has been plotted vs. the measured sensor temperature expressed directly in terms i ~Q2~~'~
of the measured Wheatstone bridge imbalance potential, U. This relationship has been derived empirically for a microbridge of the type depicted in Figure 7(c) and is plotted in Figure 13, using the least squares method in a multiple regression analysis to achieve the best fit curve. The relation can be linearized over a modest span sufficient for the purpose of the invention. Other combination configurations of heater/sensor embodiments can likewise be calibrated using known gases or gases of known k. Thus, using an off-the-shelf flow sensor of the type 7(c) in the circuit 9(a), a 4.OV pulse of 100 ms duration was used.
This yielded an approximate linear relationship between U and kg of the form kg = a4U + a5 (11) where a4 = -25.8807 and a5 = 181.778 for the above conditions.
The above then achieves the calibration of the sensor for kg. The linear approximation holds over enough of a span to provide accurate measurements.
Similar relations may be derived under other measurement conditions including additional pressure correction terms.
i ~Q2~~~~
Further details related to determining the coefficients for the algorithms to compute cp are described next. This determination requires that the measuring system be calibrated first, which consists of determining the coefficients al, a2, and a3, of the algorithm to then computer cp.
Assuming a two-dimensional model for heat transfer in the microbridge, see Figures 7a-7c, the measured sensor temperature response may be described with reference to the following processes (at zero gas flow) 1) Heat release by the heater element film.
2) Temperature build up in the heater element material (FeNi or Pt) and surrounding support material (insulator Si8N4), i.e. within the bridge material.
3) Conduction towards the sensor via a) the bridge material, and b) the fluid phase surrounding the bridge.
4) Temperature build up in the sensor material (as in heater material in item 2 above), and in the gas surrounding it by the heat arriving via the above processes.
5) Achieving a steady-state distribution of temperature.
t 2Q2 ~fl'~~
' 6) The revenue process to steps 1-5 during the start of the heater off-period.
Further assuming, for the sake of simplicity, that the specific heats of the involved gaseous and solid materials do not depend on temperature, we can approximately describe the above processes by the following expressions (see Table 2 above for symbol explanation) using the same process numbering as above:
1) Q = V2/(Ro(1 + (Th-To)) for small temperature rises.
2) The heater temperature results from balancing the heat input and output rates: Th-To =
Q/(ksAs/Ls + kgAg/Lg) with Q in watts;
the temperature Th is established in a time that is short compared to the time it takes to reach the sensor if the sensor is not identical to the heater, as in configurations 7(b) and 7(c).
3) In a truly one-dimensional case most of 50% of the released power Q eventually arrives at the sensor, since it only has two ways to go (+x and -x directions). In a two- (or even three-) dimensional case a major part of Q gets dissipated in the y and z directions, so that only a fraction, Qc, is conducted to the sensor, with a corresponding drop of the original temperature, Th, down to an intermediate temperature Tm. The sensor then experiences an energy rate arrival of r Qc = (Tm-To) (ksAs/Ls + kgAg/Lg) (12) 4) The sensor temperature rise rate is governed by the specific heat of the gas surrounding the sensor and the closely coupled material of the sensor itself so that:
Qc = (dT/dt) cpsVs + (dT/dt)cpgVg (13) The quantity measured and plotted in Figures 14, 15 and 16, is the time (dt) needed to raise the sensor temperature by an increment (dT) which is chosen by the two or more sensor resistance value markers corresponding to T1 and T2.
It is readily apparent from equation (13) that cpg could be determined for an unknown gas if the various quantities entering in Eqs. (12) and (13) were either known or measurable. It has been found, however, that even if only dt, dT, To, P and kg are conveniently measurable, the other quantities may be determined by calibration. This can be done according to an invention as follows:
For calibration, gases of known composition (preferably but not necessarily pure) and therefore of known specific heat and thermal conductivity at the used s pressure and temperature (both also measured), are brought in contact with the sensor. The effect of the pulsed heat releases is recorded in terms of the lapsed time, t2-t1, as has been described. After noting results for various gases, pressures, heater temperatures and/or heating/cooling periods, with pulses of constant temperature, voltage, current or power, the recorded time and condition data are entered into an array of data ports which can be used for automatic or computerized data processing or other number crunching techniques.
The process can be illustrated with the help of equations (12) and (13), by way of example, without excluding other, similar approaches likely to occur to one skilled in numerical analysis. With this in mind, the following ports receive data or input for various gases, pressures (and temperatures):
Ports: Y X1 X2 Inputs: cpgP/Po (t2-t1)kg t2-t1 Known and available multiple linear regression analysis (MLRA, see Figure 10) program can determine the linear coefficients a1, a2, and a3 (e. g., by matrix inversion), which, together with the above input data, t .
2~2~~~~
forms the calibrated expression derived from equations (4) and (5) to compute specific heat, cp:
cpg P/Po = al(t2_tl)kg + a2(t2_tl) _a3 (14) The determined (calibration)coefficients, of course, represent the lumped factors of several sensor properties or conditions from equations (14) and (15):
al=(Tm-To)(Ag/Lg)/(vgdT)~
a2 = (Tm-To)(Ag/LS)/(UgdT)ks~ (15) a3 cpsVs/Vg In order to minimize differences in Tm at the sensor location, the most advantageous operation from among constant temperature, voltage, current or power is chosen. The above method is demonstrated on the basis of 1) constant voltage pulses, which result in quasi square wave heat pulses released by the heater, and 2) changes in gas type (CH4, C2H6, air and 02) and pressure; the chosen configuration was 7(b).
Figure 14 shows the result of storing and plotting the dt = t2-tl and pressure data for each of the gases used, for which the cp and k values can be obtained from the open literature. This relation is linearized by applying the least squares method in a multiple linear regression analysis to achieve the best y 2~~~~~
fit line. After entering these data into the above ports Y, X1 and X2, the regression analysis program performed. The obtained result was, for a configuration as in Figure 7(b):
a1 = -16509, a2 = 3.5184 and a3 = .005392 (15a) Proof that the above calibration coefficients are valid is provided by Figure 15, for example, in which these coefficients have been used to generate the shown lines for CH4, C2H6, air and 02. As shown, the lines indeed connect and agree with all experimental points. Additional lines have been plotted with the cp and k data of the literature for other gases as well.
The final step in using this calibration method involves known means to store, write or burn in the obtained, tailored values of a1, a2 and a3 for the individual microbridge, which may be a Honeywell MICRO-SWITCH Model No. AWM-2100V, into the memory linked to it. The microsensor is then ready for use to measure the specific heat of unknown gases, provided that P and k be known at the time of measurement.
Figure 10 depicts a schematic block diagram of a device for measuring cp and k. The system includes the signal processing circuitry indicated by 170, a multiple linear regression analysis (MLRA) unit 171 for f deriving the known equation constants for the particular microbridge configuration and circuitry used, i.e., al - an, a data bank 172 for storing calibration cp and k data and an output interface unit 173.
With respect to the embodiment of Figure 10, prior to use, field recalibration may be accomplished simply by entering the P, cp and k values of the test gas into the data bank. If P cannot be measured independently of the sensor already in the subject system its errors can be incorporated as a correction in the cp and k recalibration. The measured values of U
and dt are then used as in the measurement mode to determine sensor values of k and cp. If they disagree from the entered values the constants a3 and a5 may be modified to fit the entered or book values.
This approach may be a practical one for field use, but it should be checked by using a second test gas. If that agrees, the recalibration may be completed. If not, a complete calibration of all al-a5 coefficients should be made.
It should be mentioned that in all of the above discussion the influence of temperature was not mentioned for the sake of simplicity. It is well known, however, that temperature does influence both cp and k but can be addressed, if necessary, in one of the following ways:
-3~-i 2a~~~7~
1) Controlled, (expensive and energy consuming) or 2) Compensated by special temperature-sensitive elements in the analog part of the circuit, or 3) Entered into the sensor algorithm as an additional parameter, which is sensed, e.g., by monitoring one of the many available temperature dependent resistors on the sensor. This is the preferred approach for sensing systems requiring maximum accuracy.
With respect to use of the instrument of Figure 10, the U and dt = t2-tl (and P) signals obtained for an unknown gas are processed as follows in this mode:
1) Computation of k from expression (3) using the coefficients a4 and a5 which have been stored in (or burned into) the sensor's memory after calibration, and 2) Computation of cp from expression (6).
It should also be noted that a pressure signal is also needed as a basic ingredient since cp is used here in relation to a volume of gas as opposed to k which is largely pressure independent if the sensor is used at or above .
atmospheric pressure, at which the gas mean free path is small compared to the characteristic dimensions of the involved sensor.
The graphical presentation of Figure 16 depicts heating time in milliseconds versus pressure and gas type and specifically showing curves for methane, ethane, air and oxygen. The sensing configuration of Figure 7(c) was used. In this example, the pulse height was 1.75 volts with a pulse width of 100 ms. and the heater and sensor resistance each being about 2000 ohms. Figure 17 depicts a cooling curve for the same configuration as Figure 16. Conditions were the same except that the pulse height was 4.0 volts.
Of course, the output of the device can be in any desired form including analog or digital signals, printed records, etc., after the value is obtained.
The idea to be further discussed below is based on taking a small segment of Figure 19, corresponding to the range of composition of natural gases, leading to average cp and k values near to those of methane, and to prove that even without knowing the exact composition within the chosen gas composition range, a meaningful determination of pressure, P, can be made.
Such a determination of P is needed for gas flow controls, combustion controls, and flow sensing devices (like gas meters) in order to eliminate the composition effect on the signal output of hot thin film (anemometer type) flow sensors; the use of regular pressure sensors would be too costly for such applications.
Several embodiments of this invention to obtain pressure have been conceived. Figure 20 shows an early version in which the sensed cpv in cal/(cm3C), kh and kc are combined to compute P, for gases covering a wide range: 78 natural gases and 77 peak shaving gases (50%
natural gas + 25% air + 25~ propane). No attempt was made in this embodiment to increase the accuracy by also using measurable cpv at more than one temperature. Note that the output of one sensor, cpv, is pressure sensitive, while that of the other one is not (or very little:
2.5~/atm near 1 atm); this is an important part of this pressure sensing method, which works without knowing the exact composition of the gas.
2~2~~"~~
Figure 21 which plots pressure, P, versus thermal conductivity, k, at various temperatures, shows the result of a more accurate method, although it requires more involved computations, to be discussed next.
First as is shown in co-pending application, Serial No. filed , Table 1 shows the result of deriving a number of algorithms to compute ks and cps, i.e., the properties at reference conditions of temperature, TS (and Ps), which were chosen as 60F (15.555°C) and 14.73 psia (1 atm). The actual computations were made for 15°C higher to allow for the influence of the microbridge heater on raising the average gas temperature around it. A set of over 60 natural gases used to derive these algorithms were chosen to represent a range of typical natural gases. They contain less than 2$ each of N2 or C02, no more than 0.1% 02, and no less than 85~ CH4. The chosen temperature range is from -12.2 to 45.6°C (10 to 114F).
The standard errors of the investigated algorithms vary from 5000 ppm (0.5%) down to 153 ppm, with maximum errors about 3 to 4x larger. For clarity sake the exponents of the listed polynomials have been omitted, although all are of the general form:
1/ks or 1/cps or ks or cps=A+BTb+Ckc+Dcpd+E(kTx)e+F(cpTy)f+G(dk/dT)g+H(dcp/dT)h(1) _g_ .h.
with one or more of the terms missing in order to simplify the expressions as much as possible.
The algorithms listed in Table 1 (an abbreviated Table) are preferred because the equations 3 and 4 achieved the lowest error, while equations 2 and 5 are preferred because they achieved a reasonably low error without requiring measurements at more than one microbridge heater temperature (low cost compromise).
The choices which were considered in converting the measured k and cp from the measurement* to the reference temperature (60°F, 15.555°C) values ks and cps are expressed in terms of the following functional relationships:
Table 1 CONVERSION OF k AND cp TO REFERENCE TEMPERATURE
Errors Std. Max. Log.
PPM PPM Sens.
ks - A BT + Ck + D(kT) 287 1931 2.00 +
ks - A BT + Ck + D(dk/dT) 153 +
1/cps A BT + Ccp + Ddcp/dT 165 = +
c A BT + C(c + D(kT) 197 660 1.51 - + /T) ps p The coefficients and exponents for these four preferred algorithms are as follows, with all k-values in microcal/(s°Ccm), cp in cal/(mol°C), T in °K:
t 2(~~~~'~~
Table 2 R~i.
~i.0?iLLY.~ .~ ..~ .~ ..~. ...p...
cLl ks 51.3ldb!-.005=31d1!l.dl3t1! 1.101961.ldl0=173-.l7 I1 l1! 10-s Z
1.110100 k s 61.117!.old~lss 1.1d0'3 1.5120 .91511 -lt~!)I 11.317 l c') cQ 51.7511!Id.ts111 .07dsss0! -1361.191-1.100177I.OId4~107 1.10711!
s cL) cp 1.SZ=11!-17iZ17.1 -3.01471 Sld.7ls1.1)!!1 3.19!S~Ols -;,t;1t315 s cp/eD .07113ds1~ .916741!(()~k)/tTa/T)x)-1.6661d~
s =~(Z/Za)0.3 Eq. (6) above was also discovered during this study and is listed here as an additional, very useful relation.
As shown, the top two algorithms only involve inputs of thermal conductivity properties, while the bottom one was both k and cp inputs to compute cps.
Secondly, the basis for the more accurate method mentioned above are the two algorithms eqs. (5) and (6), which compute cps and cp/cps, respectively: forming also cp/cps in the former and equating it to the latter, eliminates cps. Then, substituting the remaining cp by eq. (1) we obtain an equation for P:
P = cpv T Po VMo/To(f(k~T)9(k.T)) (7) where 260 <T <310K, Po = 1 atm, To = 273.15°K, VMS=22415(T/To)(Po/P) cm3/mol, f(k,T) and g(k,T) are i ~02~0~~
the right hand sides of eqs. (5) and (6), respectively, note that f(k,T) also contains a term with cp (see eq.
(1)) and therefore with Pc with c=1 listed in eq. (5) mentioned above, an iteration of the solution of P is needed. Results obtained with eq. (2) are as follows:
Figure 21 shows a plot of 78 natural gases at 5 temperatures and three pressures, whereby actual values of k, ks, T and TS were used to compute cp/cps with eq. (6); these were then converted to cpv/cpvs ratios via eq. (1) for three pressures and compared (i.e. ratioed) to actual values of cp/cps. The match between the points P=(cpv/cpvs)/(cp.cps) and the lines drawn for constant pressure of 0.9, 1.09 and 1.1 atm gives an indication of the accuracy of eq. (6): std. error of +254 ppm and max. error of 1077 ppm. Figure 22 shows that sizeable errors result if the incorrect reference temperature is used (-12.2.°C rather than 15.6°C).
Figure 23 presents a blown up version of the center part of Figure 19 in order to visualize the error margin achieved by the computation: note that the maximum error, obtained with half of the natural gases not used for the derivation of the equations is still within +1500 ppm.
Figure 23 presents a plot of the same gases, but now simulating a more comprehensive test of eq. (2): its solution was iterated to a value of P to within + 10 ppm by i 2~2~~'~~~
using the outputs of f(k,T) and g(k,T) from "sensed" k and T, and computing ks from eq. (8) ks = A + B Tb + Ckc + D ( kT ) d ( 8 ) which was derived earlier as eq. (2); the "sensed" value of cpv is obtained experimentally via a method described in copending applications SN 210,892 filed June 24, 1988 and SN 211,200 filed June 24, 1988 and assigned to the same assignee as the present application.
The System Thus the ability to measure pressure with a non membrane-based microbridge sensor has been shown above. In order to more fully appreciate the microbridge flow sensor system upon which the present method invention is utilized to extend the applicability thereof, the following description is supplied.
Thermal conductivity and specific heat of each fluid of interest produce characteristic transient and steady-state temperature reactions in a proximate sensor as exemplified in Figure 6.
In the preferred implementation, specific temperatures, as T1 and T2 in Figure 6, are selected as "marker" points with respect to the sensor. These marker points are used to reference the determination of the time periods, as t1 - t2, required to achieve the corresponding temperature rises) or falls) in the sensors) between the marker points. As will be discussed, the sensor or sensors are located in predetermined spaced t 202~0~~
relation to the heater or heaters, but preferably.
physically separated therefrom so that the proximate influence of the solid heater materials) is reduced and the coupling of the heater with the sensor or sensors by the fluid of interest is relatively enhanced.
The preferred embodiments of the approach of the invention contemplate disposing spaced microspec sized heating and sensing elements in a relatively static (zero flow) sample of the fluid of interest. The microsensor system or "microbridge" system, as it will be referred to herein, though not limiting, is presently preferred for several reasons. The system is extremely fast reacting, is very accurate, very sensitive because of its advantageous coupling to the fluid of interest and small and adaptable to a variety of configurations.
The microbridge chip sensor contemplated, for example, in certain embodiments preferred for the invention may resemble the form of one or more of the microbridge systems illustrated in the patents identified above. Such a system is exemplified by Figures 1-5 taken from Patent 4,501,144. A discussion of that example will now be presented as it will be helpful in understanding the present invention. While the present discussion is believed sufficient, to the extent necessary, any additional material contained in the microbridge related patents cited is deemed to be incorporated herein by reference.
t 2~~~~~~
The illustrated embodiment of Figures 1-5 contemplates a pair of thin film temperature sensors 22 and 24, a thin film heater 26 and a base 20 supporting the sensors and heater out of contact with the base.
Sensors 22 and 24 are disposed on opposite sides of heater 26. Body 20 is a semiconductor, preferably silicon, chosen because of its adaptability to precision etching techniques and ease of electronic chip producibility. The embodiment includes two identical temperature sensing resistor grids 22 and 24 acting as the thin film heat sensors and a centrally located heater resistor grid 26 acting as the thin film heater.
Sensors 22 and 24 and heater 26 may be fabricated of any suitable, stable metal or alloy film.
In Figure 8, the metal used was a nickel-iron alloy sometimes referred to as permalloy, with a composition of 80 percent nickel and 20 percent iron. The sensor and heater grids are encapsulated in a thin film of dielectric, typically comprising layers 28 and 29 and preferably silicon nitride, Si3N4, to form thin film members. In the embodiment shown in Figures 1 and 2, the sensor comprises two thin film members 32 and 34, member 32 comprising sensor 22 and 34 comprising sensor 24, each member comprising one-half of heater 26 and having a preferred dimension of 150 microns wide and 400 microns long.
t The embodiment of the system further describes an accurately defined air space 30 which contemplates air space effectively surrounding elements 22, 24, 26.
The effectively surrounding air space is achieved by fabricating the structure on silicon surface 36, thin film elements 22, 24 and 26 having a preferred thickness of approximately 0.08 to 0.12 micron with lines on the order of 5 microns wide and spaces between lines on the order of 5 microns, the elements encapsulated in a thin silicon nitride film preferably having a total thickness of approximately 0.8 microns or less, and by subsequently etching an accurately defined air space, of about 100 microns deep, into silicon body 20 beneath members 32 and 34.
Members 32 and 34 connect to top surface 36 of semiconductor body 20 at one or more edges of depression or air space 30. As illustrated in Figure 3, members 32 and 34 may be bridged across depression 30~ alternately, for example, members 32 and 34 could be cantilevered over depression 30.
Heat flows from the heater to the sensor by means of both solid and fluid couplings there between.
Of note is the fact that silicon nitride (Si3N4) is a highly effective solid thermal insulator. Because the connecting silicon nitride film within members 32 and 34 is a good insulator, heat transmission through the solid does not dominate the propagation of heat from heater f 26. This further enhances the relative amount of the heat conducted to sensing resistor 22 and 24 from heater resistor 26 by flow through the surrounding fluid rather than through the supporting nitride film. Moreover, the supporting silicon nitride film has a low enough thermal conductivity that sensing resistor grids 22 and 24 can be located immediately adjacent or juxtaposed to heating resistor grid 26. Thus, sensing resistor grids 22 and 24 are in effect suspended rigidly in the air space proximate heater resistor 26 and act as thermal probes to measure the temperature of the air near and in the plane of heater resistor grid 26.
The operation of the system in sensing air flow is described in detail in the above-referenced U.S.
patent 4,501,144. Typical circuit implementation is discussed briefly with reference to Figures 4 and 5 to add some insight. The heater control circuit illustrated in Figure 4 uses a Wheatstone bridge 46 which further typically includes heater resistor 26 and a resistor 40 in its first leg and a resistor 42, heat sink resistor 38, and a resistor 44 in its second leg.
An error integrator includes amplifiers 48 and 50 keeps bridge 46 balanced by varying the potential across it and thus the power dissipated in heater resistors 26.
The circuitry of Figure 5 monitors the resistance difference between downstream sensor 24 and upstream sensor 22. This circuitry includes a constant r ~Q~~~~
current source 52 comprising an amplifier 72 and a differential amplifier 54 further including amplifiers 68 and 70. The constant current source drives a Wheatstone bridge comprising two high impedance resistors 56 and 58 in one leg and the two sensing resistors 22 and 24 with a hulling potentiometer 60 in the other leg. The gain of differential amplifier 54 is adjusted by potentiometer 62. Output 64 provides an output voltage that is proportional to the resistance difference between the two sensing resistors 22 and 24.
To get some concept of the small size of the microbridge, the power required by heater resistor to heat such a device 200°C, for example, above ambient temperature is less than 0.010 watt. The exceedingly small thermal mass of the heater and sensor element structures, their excellent coupling to the surrounding fluid because of a high surface/volume ratio, and the thermal insulation provided by the thin silicon nitride connecting them to the supporting silicon body, and the surrounding air space, all contribute to produce a system well suited to fast and accurate sensing.
Response time constants as short as 0.005 second have been measured. Consequently, sensor elements can respond very rapidly to proximate environmental changes.
Now with reference to the implementation of the present invention, Figures 7a, 7b, and 7c, depict three slightly differing embodiments or configurations which 2~!?~~'~~.
were taught in copending applications SN 210,892 and SN 211,200 mentioned above, and are representative in terms of number and arrangement of the heaters and sensors which can be used in implementing this invention. In Figure 7a, in contrast to Figure 1, all of the elements 122, 124 and 126 are used as heaters.
Figure 7b is an embodiment which is similar to the embodiment of Figure 1 with thin film element 126 acting as heater and elements 122 and 124 acting as sensors.
The embodiment of Figure 7c, represents the preferred arrangement in which the element 122 acts as heater and element 124 acts as sensor. The effective gap and thus the thermal isolation between heater and sensor is desirably wider in the embodiment of Figure 7c.
The actual general geometric structure of the embodiments of Figures 1-3, and 7a-7c is more clearly illustrated in the scanning electron micrograph (SEM) photo of Figure 8. The precision with which the cavity and bridge elements are defined and located in spaced relation, as Figure 8 depicts, is particularly noteworthy. The SEM represents a magnification such that the indicated length of 0.010" appears as shown.
In the implementation of the invention disclosed herein particular attention is directed to (1) setting specific temperature markers in the sensor to determine the time periods needed for achieving the corresponding temperature changes, (2) using temperature 2G~~~"~
sensors which are physically separated from the heater so that the direct influence of the heater and heat conducted to the sensor other than via the fluid of interest is reduced, and (3) using a pulse which reaches at least a momentary steady-state plateau to determine k, which then is used with the transient measure to determine cp.
Figure 6 graphically depicts a square wave electrical energy pulse 130 to the heater as at 126 which results in quasi square wave heat pulses released by the heater. These in turn, result in reactive curves as at 131, 132 and 133 at the sensor which vary as described below. The pulse applied to the heater, for example, may have a height of about 4 volts with a pulse width of 100 ms. Since the heater is closely coupled through the fluid medium to the sensors, the family of curves 131, 132 and 133 resembles the shape of the input pulse 130. They show the heat response in the sensors 122 and 124. Figure 11 represents an oscilloscope trace showing temperature rise and fall versus time for dry air at atmospheric pressure. It uses a different scale for time than does Figure 6, but illustrates the curve form produced by the pulsed input. The curves generally include beginning and ending transient portions flanking a relatively steady-state central portion. The relatively quick response of the sensor allows a relatively long steady-state to exist even with a pulse t ~~a0~!
of 100 ms. Of course, the curves are affected by factors such as pressure and temperature as they influence the effective thermal conductivity and specific heat of the particular fluid of interest.
Heat flowing from the heater element or elements to the sensor element or elements is conducted both through the fluid and through the solid semiconductor element support substrate or the like. It is advantageous with respect to the measurement of k or cp of the fluid of interest that the amount of heat reaching the sensor through the solid connections be minimized so that substantially all the measured thermal effect is generated via the fluid of interest.
With respect to the transfer of heat to the sensors) some background information regarding the propagation of heat or temperature waves is presented.
The speed of propagation, v, of a one dimensional wave (if it features an exponential decay profile) is constant and given by the expression:
v - DT~a = (DT~b) 0.5~ (9) where:
a is an exponential decay (length) constant b is the rise time constant at a fixed location and DT is the thermal diffusivity.
i 2~~~~~4 A complete list of nomenclature and subscripts with units appears in Table 3, below. DT is related to k and cp by the expression DT = k/cp (10) DT, therefore, if known, may be a key to obtaining cp. The rise time constant, b, was measured to be about 4 msec. For typical gases, DT ranges from 1.7 cm2/s for He to .054 cm2/s for C3H8. Metals exhibit high values such as 1.7, 1.1 and .18 cm2/s respectively for Ag, Cu and Fe. Insulators, however, are even lower than the gases at .004 cm2/s for glass and .0068 cm2 for Si3N4 which, as discussed above, is a good insulator. The propagation speed, v, in a typical gas sample then is about (1/0.004)0'5 = 15 cm/s. This compares with (0.0068/0.004)0'5 = 1.3 cm/s for Si3N4, assuming that the same rise time constant of about 4 ms is applicable to both the one measured in the Si3N4 and the actual one in the gas.
The effect is that the influence of the temperature wave propagating from one thin film strip, that is, the heater, to a second thin film strip, the sensor, both being embedded in a membrane of Si3N4, is faster for the gas than for the Si3N4. This also supports the choice of a material such as Si3N4, since it reduces the contribution of heat flow through the solid media. This is beneficial to the accuracy of the system.
i 2~~~0'~~
Typical microbridge embodiments are illustrated by Figures 7a - 7c. They will now be explained in greater detail.
Symbol Units Exponential Decay Constant cm al-anConstant A Area of Heat Transfer to Microbridge cm2 or to Gas b Rise Time Constant at a Fixed Location C/s c Specific Heat cal/ (cm3C) p DT Thermal Diffusivity, DT = k/cp cm2/s k Thermal Conductivity cal/(smC) L Length of Thermal Conductance Path cm in Gas or Solid P Pressure of Gas psia Q Power of Heat Release Rate watts Ro Resistance at Room Temperature ohms t Time s T Absolute Temperature C
U Bridge Output or Amplified Bridge V
Output V Volume of Gas or Solid (Microbridge) cm3 v Speed of Propagation cm/s x Temperature coefficient of resistance C-1 SUBSCRIPTS
c Conduction S Microbridge or Solid g Gas o Room, Reference or Gas Temperature Without Microbridge Heating h Heater or Hot m Middle or Medium The configuration of Figure 7a involves using the same microresistance 122, 124, 126 for the heating pulse and the sensing task. In this embodiment of the resistive heater-sensor element may be one leg of a conventional resistive Wheatstone bridge in a control circuit.
Figure 7b depicts an arrangement wherein the center microresistance structure 126 is used as a heater flanked by two symmetrically located outer sensing resistance elements 122 and 124. The elements 122 and 124 are separated from the heater 126 by a narrow gap.
Figure 7(c) shows an embodiment configuration in which the left element of the bridge 122 is used as the heating element and the right element 124 as the sensor. This embodiment takes advantage of a rather large central gap to achieve improved thermal isolation between the heater and the sensor.
Figure 9 shows a modified control circuit which uses the center microresistance 126 as heater, while the sensing task is performed by the two resistors 122 and 124. The dual heater sensor configuration corresponds to Figure 7b and the circuit is representative of typical sensor/measurement circuit. Figure 9 includes a timer 140 providing square-wave electrical pulses to the heater 126. The heater couples the heat pulse to the sensors 122 and 124 in the bridge 142. The output of the bridge is connected through an amplifier 143 to a i 2~2~~~
pair of comparators 144 and 145 which operate "start"
and "stop" inputs to a counter 146 which counts 10 mHz clock pulses. The counter counts measure the time interval (t2 - tl) between temperatures T2 & T1 illustrated in Figure 6.
Figure 9a is similar to Figure 9, but more detailed. The bridge configuration is the heater -space-sensor configuration of Figure 7c. The sensor resistance arm of the microbridge is set into a Wheatstone bridge 150 at 124. Another proximate resistive arm 122 is fed a voltage pulse from pulse generator 151 to provide a heat pulse into the microbridge element 126. The Wheatstone bridge 150 also may contain a nulling balancing resistor 152 which can be used in the manner of potentiometer 60 in Figure 5 to initially zero the device. The microbridge resistor sensor 124 in the Wheatstone bridge receives the heat pulse from heater element 122 principally by thermal conduction through the surrounding fluid. Some conduction, of course, does occur through the solid microbridge substrate and surroundings.
The circuitry of Figure 9a is conventional and can readily be explained with reference to its functional operation with regard to processing the bridge output signal. The voltage output signals of the bridge 150 are amplified by differential amplifiers 153 and 154 in a differential amplifier section. The t ~~?~~'~4 imbalance signal is further amplified by a high gain amplifier at 155. The signal at 156 as is the case with the signal at 147 in Figure 9 is in the form of a DC
voltage signal, U, the amplitude of which is solely related to the thermal conductivity of the fluid of interest as will be discussed above.
The remainder of the circuitry of Figure 9a includes a DC level clamping amplifier 157 and isolation amplifier 158. The temperature level, time-related switching and counting circuitry includes comparators 159 and 160 together with Nand gates 161 and 162 having outputs which are connected to the counter timing device (not shown) as in Figure 9. By measuring the time needed for the sensor temperature to rise or fall between two or more known temperature values or markers as represented by sensor resistance or bridge voltage outputs a measure related to the specific heat per unit volume, cp of the fluid of interest is obtained. The timing device may be a conventional 10 MHz pulse counter or the like. Again, this is illustrated schematically in Figure 6.
The output signal from the Wheatstone bridge, U, represents the voltage imbalance caused by the temperature change in microbridge sensor or sensors induced by the corresponding heater pulse output.
Because the magnitude of this imbalance is related directly to the amount of energy absorbed by the sensor i 2~~~~'~~
or sensors, the amplitude of the signal is directly related to the thermal conductivity, k, of the conducting media in a manner next explained.
Figure 6 shows that during much of the about 100ms wide pulse period the temperature of the sensor reaches and maintains a constant value. During this time, the influence of the energy sink or source terms represented by specific heat are zero, which means that only thermal conductivity governs the value of the sensor temperature.
Figure 12 is a plot of temperature rise in the form of bridge output, U, (Figure 9 or 9a) using the sensing arrangement of Figure 7(b) versus time in milliseconds for various gases at atmospheric pressure.
Curves for methane, dry air, ethane and a vacuum are presented. In this specific embodiment there was a heater resistance of 800 ohms, a pulse height of 2.5 volts, and a pulse width of 100 ms. Temperature markers t, and t2 are shown on the graph. These markers relate to those of Figure 13 which shows a graphical presentation of heat up time versus pressure for several gases with a sensor-heater such as that shown in Figure 7b and using the T2-T1, marked in Figure 11.
The literature value of the thermal conductivity of several gases has been plotted vs. the measured sensor temperature expressed directly in terms i ~Q2~~'~
of the measured Wheatstone bridge imbalance potential, U. This relationship has been derived empirically for a microbridge of the type depicted in Figure 7(c) and is plotted in Figure 13, using the least squares method in a multiple regression analysis to achieve the best fit curve. The relation can be linearized over a modest span sufficient for the purpose of the invention. Other combination configurations of heater/sensor embodiments can likewise be calibrated using known gases or gases of known k. Thus, using an off-the-shelf flow sensor of the type 7(c) in the circuit 9(a), a 4.OV pulse of 100 ms duration was used.
This yielded an approximate linear relationship between U and kg of the form kg = a4U + a5 (11) where a4 = -25.8807 and a5 = 181.778 for the above conditions.
The above then achieves the calibration of the sensor for kg. The linear approximation holds over enough of a span to provide accurate measurements.
Similar relations may be derived under other measurement conditions including additional pressure correction terms.
i ~Q2~~~~
Further details related to determining the coefficients for the algorithms to compute cp are described next. This determination requires that the measuring system be calibrated first, which consists of determining the coefficients al, a2, and a3, of the algorithm to then computer cp.
Assuming a two-dimensional model for heat transfer in the microbridge, see Figures 7a-7c, the measured sensor temperature response may be described with reference to the following processes (at zero gas flow) 1) Heat release by the heater element film.
2) Temperature build up in the heater element material (FeNi or Pt) and surrounding support material (insulator Si8N4), i.e. within the bridge material.
3) Conduction towards the sensor via a) the bridge material, and b) the fluid phase surrounding the bridge.
4) Temperature build up in the sensor material (as in heater material in item 2 above), and in the gas surrounding it by the heat arriving via the above processes.
5) Achieving a steady-state distribution of temperature.
t 2Q2 ~fl'~~
' 6) The revenue process to steps 1-5 during the start of the heater off-period.
Further assuming, for the sake of simplicity, that the specific heats of the involved gaseous and solid materials do not depend on temperature, we can approximately describe the above processes by the following expressions (see Table 2 above for symbol explanation) using the same process numbering as above:
1) Q = V2/(Ro(1 + (Th-To)) for small temperature rises.
2) The heater temperature results from balancing the heat input and output rates: Th-To =
Q/(ksAs/Ls + kgAg/Lg) with Q in watts;
the temperature Th is established in a time that is short compared to the time it takes to reach the sensor if the sensor is not identical to the heater, as in configurations 7(b) and 7(c).
3) In a truly one-dimensional case most of 50% of the released power Q eventually arrives at the sensor, since it only has two ways to go (+x and -x directions). In a two- (or even three-) dimensional case a major part of Q gets dissipated in the y and z directions, so that only a fraction, Qc, is conducted to the sensor, with a corresponding drop of the original temperature, Th, down to an intermediate temperature Tm. The sensor then experiences an energy rate arrival of r Qc = (Tm-To) (ksAs/Ls + kgAg/Lg) (12) 4) The sensor temperature rise rate is governed by the specific heat of the gas surrounding the sensor and the closely coupled material of the sensor itself so that:
Qc = (dT/dt) cpsVs + (dT/dt)cpgVg (13) The quantity measured and plotted in Figures 14, 15 and 16, is the time (dt) needed to raise the sensor temperature by an increment (dT) which is chosen by the two or more sensor resistance value markers corresponding to T1 and T2.
It is readily apparent from equation (13) that cpg could be determined for an unknown gas if the various quantities entering in Eqs. (12) and (13) were either known or measurable. It has been found, however, that even if only dt, dT, To, P and kg are conveniently measurable, the other quantities may be determined by calibration. This can be done according to an invention as follows:
For calibration, gases of known composition (preferably but not necessarily pure) and therefore of known specific heat and thermal conductivity at the used s pressure and temperature (both also measured), are brought in contact with the sensor. The effect of the pulsed heat releases is recorded in terms of the lapsed time, t2-t1, as has been described. After noting results for various gases, pressures, heater temperatures and/or heating/cooling periods, with pulses of constant temperature, voltage, current or power, the recorded time and condition data are entered into an array of data ports which can be used for automatic or computerized data processing or other number crunching techniques.
The process can be illustrated with the help of equations (12) and (13), by way of example, without excluding other, similar approaches likely to occur to one skilled in numerical analysis. With this in mind, the following ports receive data or input for various gases, pressures (and temperatures):
Ports: Y X1 X2 Inputs: cpgP/Po (t2-t1)kg t2-t1 Known and available multiple linear regression analysis (MLRA, see Figure 10) program can determine the linear coefficients a1, a2, and a3 (e. g., by matrix inversion), which, together with the above input data, t .
2~2~~~~
forms the calibrated expression derived from equations (4) and (5) to compute specific heat, cp:
cpg P/Po = al(t2_tl)kg + a2(t2_tl) _a3 (14) The determined (calibration)coefficients, of course, represent the lumped factors of several sensor properties or conditions from equations (14) and (15):
al=(Tm-To)(Ag/Lg)/(vgdT)~
a2 = (Tm-To)(Ag/LS)/(UgdT)ks~ (15) a3 cpsVs/Vg In order to minimize differences in Tm at the sensor location, the most advantageous operation from among constant temperature, voltage, current or power is chosen. The above method is demonstrated on the basis of 1) constant voltage pulses, which result in quasi square wave heat pulses released by the heater, and 2) changes in gas type (CH4, C2H6, air and 02) and pressure; the chosen configuration was 7(b).
Figure 14 shows the result of storing and plotting the dt = t2-tl and pressure data for each of the gases used, for which the cp and k values can be obtained from the open literature. This relation is linearized by applying the least squares method in a multiple linear regression analysis to achieve the best y 2~~~~~
fit line. After entering these data into the above ports Y, X1 and X2, the regression analysis program performed. The obtained result was, for a configuration as in Figure 7(b):
a1 = -16509, a2 = 3.5184 and a3 = .005392 (15a) Proof that the above calibration coefficients are valid is provided by Figure 15, for example, in which these coefficients have been used to generate the shown lines for CH4, C2H6, air and 02. As shown, the lines indeed connect and agree with all experimental points. Additional lines have been plotted with the cp and k data of the literature for other gases as well.
The final step in using this calibration method involves known means to store, write or burn in the obtained, tailored values of a1, a2 and a3 for the individual microbridge, which may be a Honeywell MICRO-SWITCH Model No. AWM-2100V, into the memory linked to it. The microsensor is then ready for use to measure the specific heat of unknown gases, provided that P and k be known at the time of measurement.
Figure 10 depicts a schematic block diagram of a device for measuring cp and k. The system includes the signal processing circuitry indicated by 170, a multiple linear regression analysis (MLRA) unit 171 for f deriving the known equation constants for the particular microbridge configuration and circuitry used, i.e., al - an, a data bank 172 for storing calibration cp and k data and an output interface unit 173.
With respect to the embodiment of Figure 10, prior to use, field recalibration may be accomplished simply by entering the P, cp and k values of the test gas into the data bank. If P cannot be measured independently of the sensor already in the subject system its errors can be incorporated as a correction in the cp and k recalibration. The measured values of U
and dt are then used as in the measurement mode to determine sensor values of k and cp. If they disagree from the entered values the constants a3 and a5 may be modified to fit the entered or book values.
This approach may be a practical one for field use, but it should be checked by using a second test gas. If that agrees, the recalibration may be completed. If not, a complete calibration of all al-a5 coefficients should be made.
It should be mentioned that in all of the above discussion the influence of temperature was not mentioned for the sake of simplicity. It is well known, however, that temperature does influence both cp and k but can be addressed, if necessary, in one of the following ways:
-3~-i 2a~~~7~
1) Controlled, (expensive and energy consuming) or 2) Compensated by special temperature-sensitive elements in the analog part of the circuit, or 3) Entered into the sensor algorithm as an additional parameter, which is sensed, e.g., by monitoring one of the many available temperature dependent resistors on the sensor. This is the preferred approach for sensing systems requiring maximum accuracy.
With respect to use of the instrument of Figure 10, the U and dt = t2-tl (and P) signals obtained for an unknown gas are processed as follows in this mode:
1) Computation of k from expression (3) using the coefficients a4 and a5 which have been stored in (or burned into) the sensor's memory after calibration, and 2) Computation of cp from expression (6).
It should also be noted that a pressure signal is also needed as a basic ingredient since cp is used here in relation to a volume of gas as opposed to k which is largely pressure independent if the sensor is used at or above .
atmospheric pressure, at which the gas mean free path is small compared to the characteristic dimensions of the involved sensor.
The graphical presentation of Figure 16 depicts heating time in milliseconds versus pressure and gas type and specifically showing curves for methane, ethane, air and oxygen. The sensing configuration of Figure 7(c) was used. In this example, the pulse height was 1.75 volts with a pulse width of 100 ms. and the heater and sensor resistance each being about 2000 ohms. Figure 17 depicts a cooling curve for the same configuration as Figure 16. Conditions were the same except that the pulse height was 4.0 volts.
Of course, the output of the device can be in any desired form including analog or digital signals, printed records, etc., after the value is obtained.
Claims (15)
1. A method to determine fuel gas pressure using a non membrane-based microsensor for gases including the steps:
providing a non membrane microbridge structure (Fig.
7a-7c) supported by a substrate (20), the structure having an electrically energized heater film thereon and resistive sensor film(s) located proximate to the heater film;
locating the structure (Fig. 7a-7c) in contact with the fuel gas to be sensed for determining gas pressure;
providing an electrical energy pulse to said heater film of sufficient time duration and power to cause a resulting transient temperature rise in the fuel gas followed by a steady-state temperature level (131, 132, 133) in the fuel gas being measurable using said sensor film(s) so as to provide at least an output signal;
measuring heater power, W hc, required to achieve a constant differential, dT, above room temperature;
measuring occurrences of changes in the output signal which are characteristic of the transient temperature rise and determining an integral S for each occurrence and providing an output representative thereof;
measuring the steady-state temperature level, dU, from the output signal and providing an output representative thereof;
measuring gas temperature at the structure substrate, T g;
computing thermal conductivity, k, as a function of dU, W hc and T g (gas temp.);
computing specific heat, c p, as a function of dU, W hc, S or (dT) and T g;
determining pressure, P, according to a relation:
P = V mo (T/T o) (P o) C pv/C P
where C p = specific heat, (molar or weight) -based C pv = volumetric specific heat (measured) V mo = molar volume of ideal gases = 22415 cm3/mol @ 0ÀC and 1 atm T = sensed gas temperature in ÀK
T o = gas temperature at a reference condition of 0À or 273.15ÀK
P o = gas pressure at a reference condition of 1 atm.
providing a non membrane microbridge structure (Fig.
7a-7c) supported by a substrate (20), the structure having an electrically energized heater film thereon and resistive sensor film(s) located proximate to the heater film;
locating the structure (Fig. 7a-7c) in contact with the fuel gas to be sensed for determining gas pressure;
providing an electrical energy pulse to said heater film of sufficient time duration and power to cause a resulting transient temperature rise in the fuel gas followed by a steady-state temperature level (131, 132, 133) in the fuel gas being measurable using said sensor film(s) so as to provide at least an output signal;
measuring heater power, W hc, required to achieve a constant differential, dT, above room temperature;
measuring occurrences of changes in the output signal which are characteristic of the transient temperature rise and determining an integral S for each occurrence and providing an output representative thereof;
measuring the steady-state temperature level, dU, from the output signal and providing an output representative thereof;
measuring gas temperature at the structure substrate, T g;
computing thermal conductivity, k, as a function of dU, W hc and T g (gas temp.);
computing specific heat, c p, as a function of dU, W hc, S or (dT) and T g;
determining pressure, P, according to a relation:
P = V mo (T/T o) (P o) C pv/C P
where C p = specific heat, (molar or weight) -based C pv = volumetric specific heat (measured) V mo = molar volume of ideal gases = 22415 cm3/mol @ 0ÀC and 1 atm T = sensed gas temperature in ÀK
T o = gas temperature at a reference condition of 0À or 273.15ÀK
P o = gas pressure at a reference condition of 1 atm.
2. The method according to claim 1 in which in the step of providing a microbridge structure there are first and second resistive sensor films (122, 124) (Fig. 7) located on opposite sides of and proximate to the heater film (126).
3. The method according to claim 1 in which the electrical energy pulse to the heater film approximates in form a square wave electrical energy pulse (Fig. 6).
4. The method according to claim 3 in which the pulse width is on the order of 100 milliseconds.
5. The method according to claim 4 in which the pulse applied to the heater film has a height on the order of 4 volts.
6. The method according to claim 1 and further comprising the step of:
measuring one, the other, or both, ambient or electronics temperature, called, collectively, T e; and in which the step of computing thermal conductivity is expanded to read "computing thermal conductivity, k, as a function of dU, W hc and T g (gas temp.) while compensating for T e;" and in which the step of computing specific heat, C p, is expanded to read "computing specific heat, Cp, as a function of dU, W hc, S (or dT) and T g while compensating for T e".
measuring one, the other, or both, ambient or electronics temperature, called, collectively, T e; and in which the step of computing thermal conductivity is expanded to read "computing thermal conductivity, k, as a function of dU, W hc and T g (gas temp.) while compensating for T e;" and in which the step of computing specific heat, C p, is expanded to read "computing specific heat, Cp, as a function of dU, W hc, S (or dT) and T g while compensating for T e".
7. A method to determine fuel gas pressure using a non membrane-based microsensor for gases including the steps:
providing a non membrane microbridge structure supported by a substrate (Fig. 7a-7c), the structure having an electrically energized heater film thereon and resistive sensor film(s) located proximate to the heater film;
locating the structure in contact with the fuel gas to be sensed for determining gas pressure;
providing an electrical energy pulse to said heater film of sufficient time duration and power to cause a resulting transient temperature rise in the fuel gas followed by a steady-state temperature level being measurable using said sensor film(s) so as to provide an output signal;
measuring heater power, W hc, required to achieve a constant differential dT above room temperature;
measuring temperature rise time, dT, between two temperature markers;
measuring the sensor steady-state temperature signal, dU;
measuring gas temperature at the structure substrate, T g;
computing thermal conductivity, k, as a function of dU, W hc and T g (gas temp) ;
computing specific heat, Cp, as a function of dU, W hc, S (or dT) and T g;
determining pressure, P, according to a relation:
P = V mo (T/T o)(P o) C pv/C p where C p = specific heat, (molar or weight) -based C pv = volumetric specific heat (measured) V mo = molar volume of ideal gases = 22415 cm3/mol @ 0ÀC and 1 atm T = sensed gas temperature in ÀK
T o = gas temperature at a reference condition of 0À or 273.15ÀK
P o = gas pressure at a reference condition of 1 atm.
providing a non membrane microbridge structure supported by a substrate (Fig. 7a-7c), the structure having an electrically energized heater film thereon and resistive sensor film(s) located proximate to the heater film;
locating the structure in contact with the fuel gas to be sensed for determining gas pressure;
providing an electrical energy pulse to said heater film of sufficient time duration and power to cause a resulting transient temperature rise in the fuel gas followed by a steady-state temperature level being measurable using said sensor film(s) so as to provide an output signal;
measuring heater power, W hc, required to achieve a constant differential dT above room temperature;
measuring temperature rise time, dT, between two temperature markers;
measuring the sensor steady-state temperature signal, dU;
measuring gas temperature at the structure substrate, T g;
computing thermal conductivity, k, as a function of dU, W hc and T g (gas temp) ;
computing specific heat, Cp, as a function of dU, W hc, S (or dT) and T g;
determining pressure, P, according to a relation:
P = V mo (T/T o)(P o) C pv/C p where C p = specific heat, (molar or weight) -based C pv = volumetric specific heat (measured) V mo = molar volume of ideal gases = 22415 cm3/mol @ 0ÀC and 1 atm T = sensed gas temperature in ÀK
T o = gas temperature at a reference condition of 0À or 273.15ÀK
P o = gas pressure at a reference condition of 1 atm.
8. The method according to claim 7 and further comprising the step of:
measuring one, the other, or both, ambient or electronics temperature, called, collectively, T e; and in which the step of computing thermal conductivity is expanded to read "computing thermal conductivity, k, as a function of dU, W hc and T g (gas temp.) while compensating for T e;" and in which the step of computing specific heat, C p, is expanded to read "computing specific heat, C p, as a function of dU, W hc, S (or dT) and T g while compensating for T e".
measuring one, the other, or both, ambient or electronics temperature, called, collectively, T e; and in which the step of computing thermal conductivity is expanded to read "computing thermal conductivity, k, as a function of dU, W hc and T g (gas temp.) while compensating for T e;" and in which the step of computing specific heat, C p, is expanded to read "computing specific heat, C p, as a function of dU, W hc, S (or dT) and T g while compensating for T e".
9. The method according to claim 7 in which in the step of providing a microbridge structure there are first and second resistive sensor films located on opposite sides of and proximate to the heater film (Fig. 7).
10. The method according to claim 7 in which the electrical energy pulse to the heater film approximates in form a square wave electrical energy pulse (Fig. 3).
11. The method according to claim 10 in which the pulse width is on the order of 100 milliseconds.
12. The method according to claim 11 in which the pulse applied to the heater film has a height on the order of 4 volts.
13. The method according to claim 1 in which the integral S is computed for a cooling part in the fuel gas.
14. The method according to claim 1 in which the integral S is computed for the transient temperature rise in the fuel gas.
15. The method according to claim 1 and further comprising the step of:
providing a fluid composition and pressure dependent sensor (C pu) is combined with one that is also composition dependent but pressure independent in order to minimize a composition effect.
providing a fluid composition and pressure dependent sensor (C pu) is combined with one that is also composition dependent but pressure independent in order to minimize a composition effect.
Applications Claiming Priority (2)
| Application Number | Priority Date | Filing Date | Title |
|---|---|---|---|
| US07/458,062 | 1989-12-28 | ||
| US07/458,062 US5187674A (en) | 1989-12-28 | 1989-12-28 | Versatile, overpressure proof, absolute pressure sensor |
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| Publication Number | Publication Date |
|---|---|
| CA2025074A1 CA2025074A1 (en) | 1991-06-29 |
| CA2025074C true CA2025074C (en) | 2002-02-12 |
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| Application Number | Title | Priority Date | Filing Date |
|---|---|---|---|
| CA002025074A Expired - Fee Related CA2025074C (en) | 1989-12-28 | 1990-09-11 | Versatile, overpressure proof, absolute pressure sensor |
Country Status (6)
| Country | Link |
|---|---|
| US (1) | US5187674A (en) |
| EP (1) | EP0435611B1 (en) |
| JP (1) | JP2864291B2 (en) |
| AT (1) | ATE126884T1 (en) |
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| Publication number | Priority date | Publication date | Assignee | Title |
|---|---|---|---|---|
| EP0554095A3 (en) * | 1992-01-30 | 1994-12-14 | Honeywell Inc | Determination of fuel characteristics |
| US5753815A (en) * | 1994-11-17 | 1998-05-19 | Ricoh Company, Ltd. | Thermo-sensitive flow sensor for measuring flow velocity and flow rate of a gas |
| NL1008665C1 (en) * | 1998-03-20 | 1999-09-21 | Berkin Bv | Medium flow meter. |
| US6322247B1 (en) * | 1999-01-28 | 2001-11-27 | Honeywell International Inc. | Microsensor housing |
| WO2000039551A1 (en) * | 1998-12-24 | 2000-07-06 | Mitsubishi Denki Kabushiki Kaisha | Pressure sensor |
| US6975219B2 (en) * | 2001-03-01 | 2005-12-13 | Fisher-Rosemount Systems, Inc. | Enhanced hart device alerts in a process control system |
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-
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-
1990
- 1990-09-11 CA CA002025074A patent/CA2025074C/en not_active Expired - Fee Related
- 1990-11-30 JP JP2337006A patent/JP2864291B2/en not_active Expired - Fee Related
- 1990-12-21 DE DE69021853T patent/DE69021853T2/en not_active Expired - Fee Related
- 1990-12-21 EP EP90314135A patent/EP0435611B1/en not_active Expired - Lifetime
- 1990-12-21 AT AT90314135T patent/ATE126884T1/en active
Also Published As
| Publication number | Publication date |
|---|---|
| EP0435611A3 (en) | 1992-07-29 |
| EP0435611B1 (en) | 1995-08-23 |
| JPH03238334A (en) | 1991-10-24 |
| JP2864291B2 (en) | 1999-03-03 |
| DE69021853T2 (en) | 1996-02-15 |
| US5187674A (en) | 1993-02-16 |
| EP0435611A2 (en) | 1991-07-03 |
| DE69021853D1 (en) | 1995-09-28 |
| CA2025074A1 (en) | 1991-06-29 |
| ATE126884T1 (en) | 1995-09-15 |
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