This paper introduces a new technique for measuring induction ratios for different nozzle and combined flow geometries. The measurement technique only requires a single point velocity measurement in the secondary air inflow and a static pressure measurement in the primary air

chamber. The design if the device allows the induction ratio to be determined for different primary air nozzle arrangements with different geometries for combined air discharge outlets.

Experimentally measured data is compared with theoretical values. Four different sized circular nozzles with different outlet geometries were used to supply primary air into the device. The outlet geometries consisted of circular, slot and a rectangular shape. The results

showed that the outlet geometry has very little or no effect on the induction ratio. The most important parameter in the induction ratio is the area ratio of the nozzle and the outlet

Ruponen, M.

Tinker, J.A.

English

White Rose Research Online

promoting access to White Rose research papers    White Rose Research Online   Universities of Leeds, Sheffield and York http://eprints.whiterose.ac.uk/    White Rose Research Online URL for this paper: http://eprints.whiterose.ac.uk/7819/     Conference paper Ruponen, M. and Tinker, J.A. (2007) Novel method for measuring induction rates. In: Proceedings of the 10th International Conference on Air Distribution in Rooms. Roomvent 2007, June 13-15, 2007, Helsinki, Finland. REHVA , Helsinki, Finland. ISBN 978-952-99898-1-2  eprints@whiterose.ac.uk  Novel method for measuring induction rates    Mika Ruponen and John A. Tinker  School of Civil Engineering, University of Leeds, UK  Corresponding email: mika.ruponen@halton.com   SUMMARY  This paper introduces a new technique for measuring induction ratios for different nozzle and combined flow geometries. The measurement technique only requires a single point velocity measurement in the secondary air inflow and a static pressure measurement in the primary air chamber. The design if the device allows the induction ratio to be determined for different primary air nozzle arrangements with different geometries for combined air discharge outlets.   Experimentally measured data is compared with theoretical values. Four different sized circular nozzles with different outlet geometries were used to supply primary air into the device. The outlet geometries consisted of circular, slot and a rectangular shape. The results showed that the outlet geometry has very little or no effect on the induction ratio. The most important parameter in the induction ratio is the area ratio of the nozzle and the outlet.      INTRODUCTION    It is well a known phenomenon explained by jet theory as presented by Regensheit [1], Baturin [2], Hagström, Sirén and Zhivov [3] and Awbi [4] that as a jet of air exits a nozzle then entrainment of the ambient air takes place with a subsequent increase in flow volume. This principle may also be exploited in ventilation devices whereby the primary supply air is used to entrain room air through a finned coil or other type of heat exchanger where the room air is either cooled or heated. The combined flow of primary air and ambient air is discharged into the room via the outlet of the device. This paper presents a measurement method to determine the induction ratio for a jet of air acting in a confined space such as the ventilation ductwork in a building.   Devices utilizing the induction principle are also called jet pumps in which the main area of interest is the pressure increase of the secondary (ambient) flow. The theory of jets pumps is presented by Bonnington and King [5]. Donald and Singer [6] studied the entrainment of a secondary fluid in a water tank where the nozzle and outlet tube was submerged and presented a theoretical equation based on the nozzle and outlet diameter ratio. Ricou and Spalding [7] developed a technique to measure the local entrainment of round jets at different distances downstream of the nozzle.  Induction ratios for induction devices and active chilled beams can be measured by placing  sensors upstream and downstream of the coil to record the change in temperature of the secondary air. This information, used in conjunction with the cooling capacity can be used to determine the volume flow of the secondary air. British Standard 4954-1 [8] also defines a method for secondary flow measurement in which a two chamber technique is used. Both the above methods require sophisticated measurement equipment or a large error can be expected.    A new method is proposed in this paper that is simple and accurate. The design of the measurement device is presented together with its mode of operation and calibration procedure. Measurements are made using different sized jet nozzles and outlets. Measurements are also made using slot and rectangular shaped outlets and results are compared with theoretical models. METHOD A measurement device, later called an Induction Measurement Device (IMD), was developed as shown in figure 1 in which the primary air supply to the device was supplied via a spigot (1) into a chamber (2) which had holes to enable static pressure to be measured. Changeable plates (3) were installed on the top on the chamber which incorporated the primary air nozzles. The nozzles jetted primary into a mixing chamber (4). A combined flow outlet (5) was located at a specified distance away from the nozzles. The secondary air flow into the device was via an inlet (6). The device also had a housing to control the secondary air flow (7) but this was not used in this study. Figure 1. Construction of the induction measurement device. For measurement purposes, four nozzles sizes were manufactured according to ISO 5167-1 [9]. An example of the nozzle geometry is shown in figure 2. Three sizes of secondary air inlets were used having throat widths of 40, 60 and 80mm. The different sizes were used to investigate the effect of throat width on entrainment ratio. After initial testing and calibration only the 80mm throat width was used as the narrower widths gave low flow values when compared to corresponding theoretical values as shown in figure 3. throat Width (mm) Figure 2. Geometry of the nozzle 80 60 40 SQRT(Ax/Ai)2 3 4 5 6 7 8 9 10Induction Qx/Qi Figure 3. Induction ratios for different secondary air inlet throat widths The design of the IMD also allowed adjustments to be made to the distance between the nozzle and the start of combined flow outlet. The distance was set to allow for maximum divergence of the primary air jet prior to it entering the combined flow outlet zone. CALIBRATION The flow rate at a nozzle was determined by measuring the static pressure in the primary air chamber. A filter mat and perforated metal plate was placed into the primary air chamber upstream off the nozzles to ensure an even flow of air into each nozzle. The chamber had three pressure tappings; one in each end and one in the middle. It was quickly established that the pressure at each measurement point was the same and so thereafter only one measurement point was used as in figure 4a. a) b) Figure 4 a) Measurement of static pressure inside the primary air chamber, b) Velocity measurement at the secondary air inlet throat The primary air flow through the nozzles was calibrated using an orifice plate. Correlation between the measured flow rate at the orifice plate and measured static pressure in the chamber was established and used to determine the actual primary air flow rate. Figure 5. Secondary flow measurement calibration arrangement The operation of the primary air chamber was reversed to enable the secondary air flow calibration as shown in Figure 5. Instead of supplying air to the chamber it was used to extract air from inside the device. The combined flow outlet was removed from the device and replaced by piece of sheet metal to ensure that the airflow into the device was only through the secondary air inlet. The volume flow of the extracted air was measured using an orifice plate and pressure differential meter. The volume flow was controlled using a frequency converter controlled fan. A unidirectional anemometer was used to measure the air velocity at the centre of the throat at three different longitudinal locations as shown in figure 4b. Air-tightness in the device was ensured by taping all the joints with duct sealing tape. After the initial test results were available from the different locations, the number of measurement locations was reduced to one as no notable difference in results was found between them. A set of measurement was then made starting at a high air flow rate. The same procedure was then repeated but in the reverse order. The results are given in figure 6 which shows the correlation between the velocity reading at the secondary air inlet throat and the volume flow extracted through the orifice plate. y = 0.0273x - 0.009 R2 = 0.9978 0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8 0.9 0 5 10 15 20 25 30 35 Flowrate at Orifice Plate (l/s) Velocity at throat (m/s)Measured velocity Linear (Measured velocity) Figure 6. Correlation between throat velocity and volume flow. MEASUREMENTS Measurement procedure Induction ratio measurements were made for circular combined flow outlets according to Table 1. In the table, the letter C after case number stands for a circular combined flow outlet geometry. Test cases for rectangular shaped combined flow outlets were made according to Table 2. Letter L after the test case number stand for the slot type combined flow outlet geometry in which several nozzles supply into one rectangular or slot outlet. Letter R stands for the combined flow outlet part in which a single nozzle supplies a rectangular shaped outlet. The distance required between the nozzle and the start of outlet part was calculated and set to allow for maximum divergence without recirculation of any air back into the mixing chamber (i.e. jet divergence + nozzle diameter should be less than diameter of the circular outlet or side length for rectangular outlet geometries). The airflow direction was also tested using a smoke trace supplied via the nozzles prior to each measurement. The distance was accepted to be correct if no recirculation of the smoke was detected inside the device. An anemometer was placed in the same position as in the calibration measurements to measure secondary air velocity through throat of secondary air inlet. The primary air flow rate was controlled using a frequency converter controlled fan and pressure differential in the primary air plenum. Table 1. Test cases for circular outletsOutlet Nozzle diameter diameter Diameter Case D (mm) d (mm) ratio D/d 1C 32 8.49 3.8 2C 32 6.00 5.3 3C 32 4.24 7.5 4C 32 3.00 10.7 5C 46.4 8.49 5.5 Each test case was allowed to stabilize for a period of five minutes before any measurements were recorded. After this, the air velocity was recorded over five by three minute periods and averaged. Table 2 . Test cases for rectangular outlets Outlet Nozzle Outlet Nozzle Nozzle width spacing area diameter area SQRT Case (mm) (mm) (mm2) d (mm) (mm2) (Ax/Ai) 6L 25 25 625 6.00 28.27 4.7 7L 25 50 1250 6.00 28.27 6.6 8R 50 48 2400 6.00 28.27 9.2 Theoretical results The induction of ambient air into a jet is relative to the distance in outlet diameters and is constant regardless of the physical size of the jet. Therefore a small nozzle will induce more ambient air for same physical distance [1- 4]. This is also in agreement with Donald and Singer [6] who obtained a correlation between mass flux and nozzle diameter by assuming that the momentum across any radial section of a jet cone equals that at the nozzle exit. The resulting equation may be expressed as: QxVx = QiVi (1) Where -Qx is combined volume flow rate (l/s);Vx is combined volume flow velocity (m/s) and with subscript i is the same for the initialconditions at the nozzle exit. From continuity of flow, the following equations are obtained:4Qx and 4QiVx = 2 Vi = 2 (2 and 3) πD πd Where œ D is diameter of combined flow outlet (mm) d is nozzle diameter (mm). By combining equations 2 and 3 -Q x D = (4) Q i d In this study a further assumption is made in that the diameter relationship should comply with the rectangular shapes area ratio under the square root as follows -. Q x A x= (5) Q i Ai Where œ Ax is the cross sectional area of the combined flow outlet (mm2 ) and Ai is nozzle cross sectional area (mm2 ). Equations 4 and 5 were then used to calculate the theoretical induction ratios for different geometries. In the figures 6 and 7 the measured and theoretical results from equations 4 and 5 are compared. RESULTS Test cases 1 œ 5 were all made using a circular outlet. The tests were started using circular combined flow outlets to minimize the uncertainty that other geometries may have had on the results. Test cases 6 and 7 were made using slot type combined flow outlets in which each slot was supplied by several nozzles. In cases 6 and 7 the same size outlet part was used, but the nozzle spacing was different. In these cases the divergence of the jet in the longitudinal direction was limited by the air flow from an adjacent jet. For maximum divergence in that direction, nozzles were spaced at 25mm and 50mm as presented in Table 2. In the cross-wise direction, the combined flow outlet walls limited any divergence. In test case 8, the combined flow outlet was partitioned into small rectangles so that the divergence of the jets was limited by the enclosing walls. The results of different test cases are presented in Figures 7 and 8. The induction ratios are presented after being normalized (i.e. the measured results are compared to theoretical results using Equation 4 for circular outlets and Equation 5 for slots and rectangular outlets). 0.60 0.65 0.70 0.75 0.80 0.85 0.90 0.95 1.00 Normalisedresult(Qx/Qi) 1C 2C 3C 4C 5C Experiment Figure 7. Normalized measurement results for circular outlets In Figure 7, the experimental results are shown to be in good agreement with theoretical results for circular outlets. An assumption made in calculating the theoretical results was that the momentum of the jet is the same for any cross section of the jet. In the experiment a small Normalised result(Qx/Qi) loss of momentum occurred in the form of a flow restriction. For test cases 1 to 4 results are approaching the theoretical value as the size of the nozzle reduces. This might be due to lower momentum loss. Even though smaller nozzle sizes have higher induction ratio for the same combined flow outlet geometry, the actual volume flow of the secondary air is less. This would result in lower flow restrictions and therefore better agreement with the theoretical results. Results for the slot and rectangular outlets are shown in Figure 8 and are very similar to those obtained for circular outlets. The experimental results are again in good agreement with theoretical values. In test case 8, the measured value is slightly lower than for cases 6 and 7. A possible explanation of this could be the increase in friction effected by the partitioning walls in the combined flow outlet. 1.00 0.95 0.90 0.85 0.80 0.75 0.70 0.65 0.60 6L 7L 8R Experiment Figure 8. Normalized measurement results for rectangular outlets CONCLUSION In this study, a novel method for induction measurement has been presented. The theoretical results are based on the assumption of constant momentum at the nozzle and exit plane of the of the combined flow outlet. Experimental results show good agreement with theoretical but tend to be slightly lower but within 0.92 œ 0.99. There can be many reasons for this discrepancy, but the most likely is the flow restriction that occurs under all flow conditions in the conduit. The results presented for the circular outlets in figure 7 show a clear trend of higher nominal induction rates for reducing nozzle size. For the smallest nozzle, the mass flow rate through the device is the smallest and hence the flow restriction is also the smallest. The effect of outlets geometry has also been presented in the paper and the results clearly show that the shape of the cross section of the outlet has very little or no effect on the induction ratio. The diameter ratio of the nozzle and the outlet can be clearly be extended to cover other shapes when the square root ratio of the outlet and nozzle area are used as proposed in equation 5. ACKNOWLEDGEMENT The writers would like to thank the Finnish Technology Agency (TEKES) for funding this project as well as the financial and other support given by Halton Oy. REFERENCES 1. Regenscheit, B. 1970. Die Archimedes-Zahl Kenzahl zur Beureilung von Raumströmung. Gesundhheits Ingenieur 91(6). 2. Baturin, V. V. 1972. Fundamentals of industrial ventilation, 3rd English edition. Pergamon press. New York. 3. Awbi, H. B. 1991. Ventilation of Buildings, Routledge. London. U.K. 4. Hagström, K. Siren, K. Zhivov, A.M. 1999. Calculation methods for air supply design in industrial facilities. Helsinki University of Technology, HAVC Laboratory, Report B60, Finland 5. Bonnington S.T., King A.L., (1972), Jet Pumps and Ejectors; A State of Art Review and Bibliography; Second Revised Edition, BHRA Fluid Engineering, England 6. Donald, M. B., Singer, H. 1959. Entrainment in Turbulent Fluid Jets. Transactions of Institution of Chemical Engineers. U.K. 7. Ricou, F.B. Spalding, D. B. 1961. Measurements of Entrainment by Axisymmetrical Turbulent Jets. Journal of Fluid Mechanics. Volume 11. pp. 21-32, U.K. 8. BS 4954-1. 1973. Testing and rating induction units for air distribution systems œ Part 1. British Standards Institution. London. U.K. 9. ISO 5167-1. 1991. Measurement of fluid flow by means of pressure differential devices œ Part 1. International organization for standardization. Switzerland. 

Novel method for measuring induction rates

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Novel method for measuring induction rates

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