|List of Symbols:
astreamline= acceleration along a streamline [m/s2]
C = discharge coefficient [unitless]
dƒ = primary contraction diameter during actual flow conditions [m]
Dƒ = pipe diameter during actual flow conditions [m]
ƒshear = fluid shear stress [N/m2]
glocal = local gravitational constant [m/s2]
Helevation = elevation above a datum [m]
Pflow = pressure at flow conditions [Pa]
ΔP = pressure differential [Pa]
qmass = mass flowrate at flowing conditions [kg/s]
qvolume = volumetric flowrate at flowing conditions [m3/s]
Y1 = adiabatic expansion factor [unitless]
ρflow= density at flowing conditions [kg/m3]
The quantification of volumetric or mass flow is one of the most difficult measurements to make — even in a well-characterized fluid. This is made more difficult in a demanding environment, such as a cryogenic fluid. The value determined often has great impact on the work being conducted, particularly in liquid propulsion systems. Commonly used instrumentation measurement techniques include the use of differential producers, such as Venturi-, flow nozzle-, and orifice plate-type devices. The performance of these instruments in actual application in transient multiphase cryogenic systems is typically one to two orders of magnitude poorer than manufacturer specifications. And while differential producer-based systems are commonly applied in such environments, they have inherent theoretical limitations that affect their accuracy, reliability, and repeatability. These limitations are discussed hereafter.
Volumetric & Mass Flow
Fundamentally, volumetric flow or mass flow is the amount of volume or mass, flowing through some sort of channel per unit time. The channel may be open (trough) or closed (pipe), but must allow for the passage of fluid.
Conceptually volumetric flow and mass flow are simple. However, a closer look at each term shows the difficulty of making a valid measurement.
The cross-sectional area of a pipe tends to be the easiest to account for. The associated errors directly relate to the error in the physical measurement of diameter. Care must be taken to account for changes in the cross-sectional area (or diameter). These may include: thermal contraction, caking or debris accumulation, etc. Secondary effects, such as pressure bulging and pipe eccentricity or concentricity, and the effect of roughness changes with time on the velocity profile (Reynolds number) must also be considered to further improve the measurement.
|Figure 1. Pressure differential devices use a geometric flow perturbation to create a pressure difference — (a) Venturi tube, (b) flow nozzle, and (c) orifice plate. Drawings adapted from .|
Volumetric and mass flow is often taken as a bulk property and therefore the velocity is often reduced to a bulk or net fluid velocity. Measured values for velocity are difficult, particularly in cryogenic fluid systems. Realistically the flowrate is not uniform across the flow front (or flow stream tube). Any direct flow measurement, will at best, be an average across the entire streamline. Differential producers do not rely on a direct velocity measure, but as will be shown below, critical assumptions are made to account for it.
The measure of density is difficult in a moving environment, particularly without disturbing the flow path. Fluid systems that have multiple thermodynamic phases commingling, such as cryogens, are especially problematic. Generally the density in gaseous systems can be controlled with a fair amount of accuracy , while in cryogenic flows it is not uncommon for the liquid, gas, and possibly solid phases to coexist and may even include multiple species fluids . Table 1 shows the density variations between the thermodynamic phases. For example, if 1 percent of the volume in a pure liquid oxygen flow were converted into O2 gas it would displace approximately 2.5 times its volume of the liquid. This would result in a dramatic error in mass flow. Surprisingly, density plays a crucial role even in the volumetric flow equations of differential flowmeters even though it does not appear in Equation 1.
Volumetric and mass flow can be measured with a variety of methods. Most involve direct contact or interaction with the flow. This interaction leads to an exchange of energy. This addition of energy hastens density change, or worse, gas generation in the fluid flow.
Differential producers or pressure differential devices, most commonly represented by Venturi-, flow nozzle-, and orifice plate-type devices, infer a mass flow value by way of two pressure measurements in different regions of the flow. The key is to pick two regions of the flow that are convenient to sample while maintaining a wide pressure differential.
Figure 1 illustrates some common pressure differential geometries. In addition to the classic flow bodies shown in Figure 1, pressure differential devices can also vary the flow direction instead of the cross-section to achieve a pressure change; such as a pipe elbow or other bend, where the pressure is measured across the inner and outer bend radii. Equations may be derived to translate these two pressure values, or more aptly their difference, to a mass flow.
Insight into the embedded approximations in mass flow sensors can be seen in the derivation of the differential flow sensor working equation [1, 2, and 5]. First, a one-dimensional flow assumption is invoked to clarify the calculations. Only the element of flow in the downstream direction is used to contribute to the overall flow. On one hand, this makes some logical sense. A flowing system must be flowing in some direction constrained by the pipe. What it precludes are losses and
turbulence, that can change the kinetic energy of a flow either causing frictional losses (pressure head loss) or, in the case of a cryogenic fluid, density changes. Additionally, the fluid must be incompressible. Again, for fluids it is fair to assume that changes in density versus pressure may be somewhat neglected if the flow is purely in the liquid phase. How valid is it to describe realistic flows as pure liquid phases? In cryogenics, particularly, the fluid is often flowing at or near its boiling point. While the liquid phase component of the flow may be incompressible, the gas phase component obeys gas compression equations (i.e., ideal gas law or Van der Waals). This directly relates the density to the temperature and pressures of the fluid. Using an element or slug of fluid (Fig. 2), Newton’s second law may be used to build a balanced force equation .
Where the net pressure force is,
the force due to the elevation change,
the viscous shear force,
and the mass acceleration term of the slug,
This equation does embody all relevant forces, such as shear, for use in real flow systems. Assuming a streamlined flow-front conveniently thins Equation 3. With the addition of a constant density assumption one can arrive at Bernoulli’s equation.
Differentiation of Equation 3 can be reduced to a more familiar generic solution for volumetric and mass flow.
With Y1 as the adiabatic expansion factor, C as the discharge coefficient and df, Df as the primary contraction diameter and pipe diameter during actual flow conditions. These parameters are described in the following section.
It is important to describe the various correction terms that play a role in Equation 4. To begin with, the discharge coefficient, C, is a lump-sum correction term that provides the “fix” from the theoretical system to the real system. The discharge coefficient may be calculated depending on the type of flowmeter. These vary in error from about 0.4 for an uncalibrated meter to 2 percent , depending on meter type. This error is a systematic error and is in addition to any other errors (systematic or random). The discharge coefficient can also be determined through calibration. This must be done in the exact same system and under the exact same conditions and environments that the sensor will be used. Rarely is this accomplished, but instead manufacturer calibrations are taken from “like” systems. Particularly in cryogenic devices, water is used as a calibration fluid. The discharge coefficient for the meters shown in Figure 1 range from 0.6 for the orifice to 0.995 for the Venturi and nozzle. The abrupt change in streamlines, however, results in substantial additional pressure loss for the nozzle and orifice. This sometimes results in the unwanted flashing to a vapor.
|Figure 2. Description for incompressible fluid equation 3. Adapted from “Flow Measurement Engineering Handbook,” Figure 9.1 .|
The term Y1 describes the gas expansion of the fluid, which can be an empirically derived function or theoretically determined, such as the adiabatic gas expansion factor. For an assumption of purely liquid flow this becomes unity. This is even assumed in cryogenics at or near their boiling points. The slightest multiphase component can seriously undermine this approximation. Normally this term is ignored, and its effects are hidden in the discharge coefficient. The fallaciousness is that when the discharge coefficient is used to calibrate the system, it is assumed that the system is corrected over a range of environmental conditions. In reality, the gas expansion term may vary depending on the amount of vapor present this may continuously fluctuate with slight differences in environmental conditions from calibration.
As mentioned earlier, the physical diameters are df, Df. These are the respective bore and pipe diameters. They describe the expansion and contraction of the flow container (pipe and meter bore) due to pressure and temperature effects. These are particularly critical in cryogenic systems where extreme low temperatures cause considerable material contraction. These coefficients require accurate pressure and temperature information in addition to an accurate understanding of the fluid interaction with the pipe material. There is also the added assumption that the temperature and pressure in the pipe or bore match closely with the pressure or temperature sensor location (see below).
The pressure differential, ΔP, is only as valid as the pressure measuring device. Since the mass flow or volumetric flow is determined from a differential pressure measurement it is critical that this value be well characterized. Ideally, the pressure sensors are properly calibrated and corrected for environmental effects such as temperature. Additional factors may include frequency response effects related to the response of the pressure sensor and mounting offset usage (sense lines) .
Lastly, rfluid, the fluid density term, describes the density of the fluid. There are numerous tabulated values for various fluids under many thermodynamic conditions. These were developed from highly accurate equations of state that accurately define the density the fluids properties from temperature and pressure measurements. The use of flow computers to compute the necessary fluid properties using these state equations is becoming increasingly more popular. These methods, however, are not foolproof. Small errors in the measures of pressure and temperature can adversely affect the density generated.
Temperature probes may be located near the differential device and can provide a localized measure of temperature. Unfortunately at the temperatures considered here they tend to behave as heat pipes, coupling the environment outside the pipe into the fluid. They also tend to have low response times, on order of seconds , leading to latencies under non-steady state conditions. Pressure sensors, on the other hand, tend to average over large fluid volumes, thereby under-representing jumps or steps in the fluid state under a transient condition.
For flow conditions where the thermodynamic state is well defined the computation-based approach to density enables a high-accuracy flow measurement. Careful consideration must be made when the fluid state is not well understood or transient and/or multiphase conditions limit the validity of the supporting instrumentation.
In addition to the theoretical limitations inherent to these devices, differential flowmeters have been tested in characterized in multiphase transient environments. Errors increase dramatically for any deviation from single-phase and steady-state flow conditions. Work at NASA’s Johnson Space Center on flow sensor feasibility has shown errors in using Venturi-type devices ranging from 10 percent to 40 percent in transient and multiphase cryogenic flows .
More often than not Web- or pamphlet-based flow discussions begin with Bernoulli’s equation to derive the necessary working equations. Before Bernoulli’s equation can be applied to a fluid environment critical concessions have to be made that limit the applicability and accuracy of differential flowmeters. Clearly the critical measurement component lacking is understanding the thermodynamic and density conditions of the fluid. While quite acceptable in more benign fluid environments, differential-pressure flow devices are greatly limited in transient cryogenic fluid applications. The user must take care when using such devices in these difficult flow conditions.
Valentin Korman, Ph.D., of Madison Research CorporationWFI, has 10 years of sensors, instrumentation, and testing research development experience. Recent efforts have focused on evaluation and development of cryogenic flowmeter technologies. Dr. Korman can be reached at email@example.com or (256) 544-4625
John Wiley, of NASA Marshall Space Flight Center, has 17 years test experience with cryogenic propulsion systems, as well as research and development of advanced sensors for propulsion applications and experience with data validation and electrical and mechanical systems.
Richard W. Miller, Ph.D., of R.W. Miller & Associates, Inc., is a consultant to industry in various flow system and flowmetering areas. He was previously senior consultant with the Foxboro Company and serves, or has served, on many standards and technical committees, both nationally and internationally. Dr. Miller is the author of the “Flow Measurement Engineering Handbook” (McGraw Hill).
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2. Richard W. Miller, Flow Measurement Engineering Handbook, 3rd Edition, McGraw-Hill, 1996.
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4. D. R. Lide, CRC Handbook of Chemistry and Physics, 71st Edition, CRC Press, 1991.
5. Korman V., Gregory D. A., and Wiley J. T. Mass Flow Measurement in a Cryogenic System using a Fiber Optics-Based Dispersion Sensor, Propulsion Measurement Sensor Development Workshop, Huntsville, AL May 2003. Proceedings.
6. Wiley J. T., Korman V., Vitarius P. T., and Gregory D. A., Acoustic Wave Propagation in Pressure Sense Lines, Presented at 39th AIAA/ASME/SAE/ASEE Joint Propulsion Conference, 2003, Proceedings.
7. Nanmac, Comparison of Temperature Sensor Response Times,
8. R.S. Baird, Flowmeter Evaluation for On-orbit Operations, NASA TM-100465, Johnson Space Center, August 1988.