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8/6/2019 5965_48_40_a Study of Turbulence Induced Forces Acting on the Blobe Valve_2005
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A Study of Turbulence Induced Forces Acting on a Globe
Control Valve Operating at Small Opening
A. Hassan1. and A. Sharara2
Abstract - Under certain opening conditions and partial opening of control valves, the piping
systems occasionally suffer large vibrations. To understand the valve instability that is responsible for such vibrations, experiments and CFD simulations were performed. As a result of the study of
the turbulence flow through a single seat globe valve operating at small openings, it was found
that a complex three-dimensional flow structure (valve attached flow) sets up in the valve regionleading to high pressure variations in the valve trim region. CFD calculations showed how a jet
may impinge on the roof of the valve body and cause a large-scale recirculation region in the pipedownstream of the valve. Moreover, it was found that the smaller valve opening, the larger the
exciting force acting on the valve stem. The harmful effect of the fluid flow forces (exciting forces)
is very much pronounced at relatively smaller valve opening. The simulation results for turbulent
flow with k model were more accurate than the k model. In addition, k model was
simpler and faster in convergence than the k model.
Keywords: Control valves – Turbulent – Simulation – Computational fluid dynamics.
I. Introduction
Control valves are used to control volumetric flow
rates and keep the regulated process variable as closeas possible to the desired set point. One of the most
common types of control valves is the single seat globe
valve. It consists of three main components: body, trim(which made up of the plug and seat), and actuator.
The trim of the control valve is responsible for theinherent valve flow characteristics. Different flow
conditions require different shapes of the plug and seat
to achieve optimum flow control. In severe serviceapplications; control valves are equally crucial for
safely dissipating high process fluid energy levels toavoid valve and piping damage from acoustic noise,
vibration, cavitations and erosion. To varying degrees,all of these potentially damaging phenomena scale with
flow velocities in the valve and valve trim, leading
some valve manufactures to recommended specific
limits to fluid kinetic energy )EK ( in the valve trim.
More recently, designers of fluid handling equipments
are using CFD simulation for product development
and optimization. In the present study, CFD has beencombined with experimental work to analyze the flowthrough globe control valve with a flat-faced plug,
operating at small opening.
II. Literature Review
Despite of the importance of control valves, a little
research work has been published on control valvedesign, especially for the globe control valves. In an
attempt to avoid a host of valve problems, Miller [1]
proposed applying valve trim maximum EK criteria
including component vibration, breaking parts,excessive aerodynamic noise, trim and/or valve pitting
and erosion caused by liquid cavitations or flashing andsurface erosion by solid particulate. Based on
operational experience, Miller and Stratton [2]
presented an allowable trim EK limit for a given
control valve application that depends on theapplication service conditions. The criterion involves
limits on the fluid EK existing from the valve’s trim.
They advocate a kPa485 limit to a clean flowing
process fluid, but suggested a kPa275 limit for
cavitating and multiphase trim flows. Hardin et al [3]studied three different plug design cut off, concave and
hybrid to eliminate the flow-induced instability of steam turbine control valves. They used a steady state
CFD model and found that the hybrid plug design is
the most convenient shape for the presented case.Wojtkowiak and Oleśkowicz-Popiel [4] carried out
numerical and experimental investigation on the flow
characteristics of butterfly valves. Flow patterns and pressure distribution in the disk vicinity were obtained.
The computational results, obtained from the standard
k-ε turbulence model, agree qualitatively with the
results of the experimental study. It is likely that moresophisticated turbulence model will yield quantitatively
more accurate values. Using the FLUENT code, Kim
[5] investigated a three dimensional numericalsimulation to analyze an incompressible flow through
the partially-opened thin-flap disk butterfly valve.
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Chern and Wang [6], conducted a 3D numerical
simulations and experiments were conducted toobserve the flow patterns and to measure performance
coefficients when V-ports with various angles were
used in a piping system. Three V-ports with angles 30deg, 60 deg, and 90 deg were studied. It was found that
V-ports with angles 30 deg and 60 deg make the flowrate proportional to the valve opening. However, V-
ports increase the pressure loss between the inlet and
the exit of a ball valve. Davis and Stewart [7] studiedthe performance of a single seated globe valve by
applying Fluent CFD code. They showed that the
valve characteristics could be accurately predictedusing axisymetric flow models over most of the plug
travel. Hong et al [8] performed a numerical simulationfor the cavitating flow in hydraulic conical valves. The
structure of the valve was simplified as two
dimensional axisymmetric model. They found that the
cone shape have a considerable effect on the intensityof the cavitation. Amirant et al [9] studied theoretically
flow forces on an open center directional control valve.
The results showed that the flow force increases with
increasing the flow rate. Oza et al [10] presented aCFD model for a globe valve in oxygen applications.
They used both k and k models of turbulence
through the numerical computations. The simplifiedaxisymmetric model was used to predict the inherent
valve characteristic. Their results showed that the
k turbulent model is more suitable for boundary
level flow.
In the present study, the fluid flow around a single
seat globe valve will be treated as a three-dimensional
flow to focus on the details of the flow variations in the
valve region. An experimental study and CFDsimulation are conducted to understand the cause of the
fluctuations. The fluid flow force acting on the valvestem is measured and compared with the obtained
values from the numerical study to verify the numericalmodel.
III. Experimental Facility
An experimental test rig was designed on the basisof closed loop flow system. The test setup in Fig.1 is
driven by a 7.5 hp centrifugal pump and is capable of
providing hr m48 3 of water flow. The test rig
generates 400 kPa (4 bar) across the test valve at flow
rates up to 30 m³/hr. the rotational speed of the pump
may be adjusted via a frequency inverter to obtain adesired value of the water flow rate. The test section is
situated at the fully developed flow area and the back pressure can be controlled using a butterfly valve
downstream of the test section. A calibrated orifice
flow meter is used to measure the flow rate during the
experiments. Pressure transducers, which candistinguish millisecond fluctuations, are mountedupstream and downstream the globe valve to measure
the pressure fluctuations caused by the valve. The
upstream pressure 1P and downstream pressure 2P are
measured from static wall tapings located 5 pipediameter upstream and 11 pipe diameter downstream
of the valve. The mounting of the pressure transducersneeded special attention to avoid an influence to the
flow field [11]. The bonnet of the tested valve was
modified from a standard type (Fig.2-a) to an extendedtype (Fig.2-b) which included an S-type load cell tomeasure the flow net force acting on the valve and to
transmit it to the valve body. The sensing elements of the load cell, those subjected to bending moments.
Bending elements offer high strain level at relatively
low force, which makes them ideal for low capacityload cells. In the proposed design of the load cell, there
are two surfaces subjected to equal strains of oppositesign. This offers convenient means for implementing a
full bridge circuit, while temperature compensation is
relatively easy. Bending as a measuring principle offersexcellent linearity of the S-type load cell, which was
used in the experiments to measure the flow net force.Using CIO-EXP-GP signal conditioning board, the
time history signals have been collected and
transformed to DAS08-AO data acquisition card via a
37 pin connector cable.
III.1. Test Conditions
The hydraulic test and measurements have been
made at room temperature with flow rate up to
hr /m403 and a valve opening up to 40%. The
opening of the control valve was set using a dial gauge
indicator, which has a resolution of 0.01 mm. Thevalve’s opening was 5, 10, 20, 30, and 40 %;
respectively, and the maximum valve travel was 23
mm. The maximum pump outlet pressure was 5.7 bar,while the minimum back pressure of the valve was 0.3
bar.
III.2. Valve Characteristics
There are two important control valve parameters,
the overall flow coefficient vC and the relative valve
capacity dC . The flow coefficient vC is a measure of
valve capacity. It is given by the ISA standard S75.01
[12] for incompressible, fully turbulent, noncavitating
and nonflashing flow as
P
GQ6.11C f
v (1)
where f G is the specific gravity of the fluid. In the SI
system of units, the units of vC are
))kPa/()hr /m(( 5.03 . Equation (1) is applicable to fully
turbulent flow field for which valve parameters becomes independent of the Reynolds number. The
relative valve capacity factor dC is a measure of the
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Entrance Pipe
Tested
GlobeValve
Butterfly
Valve
WaterTank
Isolation Ball ValveFilter
Isolation Ball Valve
Long
RadiusBend
Pump
Flexible
Joint
OrificeMeter
Upstream
PressureTransducer
DownstreamPressure
Transducer
FlexibleJoint
(a) Outline of experimental apparatus
(b) Overhead view of the test loop
Fig. 1. The experimental test rig.
valve capacity relative to its nominal pipe size pD , it is
given by
2 p
vd
)D0394.0(
CC (2)
and has units of )mm/()kPa/()hr /m( 25.03 . Values of
dC do not normally exceed 11, see [7]. The inherent
valve characteristic is a plot of vC versus percent
opening of the valve, which represents an indication
for how the flow rate will change with a change in
percent opening of the valve. The percent opening of the valve is a measure of how far the plug is stroked
relative to its maximum stroke length. The flow
coefficient vC is experimentally determined for
different valve openings or positions. For a constant
valve opening, ten test runs were made for turbulent
flows at high Reynolds numbers such that the flow
coefficient should remain constant, 5e 101R . Runs
were made at levels of heavy cavitation were avoided
because of the effect of cavitation on vC . The flow
coefficient was then calculated from the average of the
test runs at a constant valve opening, after excludingthe largest and smallest values. Valve position is
expressed in terms of percentage of full opening
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(a) Standard (b) Modified
Fig. 2. Bonnet design of tested valve
)mm23( . For the purpose of test repeatability, valve
opening was always set and measured by opening the
valve to a given position. The experimental results
illustrated in Fig.3 show the inherent valve
1- Valve Body
2- Seat3- Plug
4- Stem
5- Bonnet6- Side Rod
7- Load Cell8- Lower Square Plate
9- Rigid Spacer 10- Nut
11- Side Guide12- Upper Square Plate
13- Handle
14- Dial Gauge
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characteristic for the valve under investigation.
Accordingly, the test-valve was found to be of quick-opening type.
Fig. 3. Inherent valve characteristics
IV. Dimensional Analysis
The flow force acting on the valve stem 'F' depends
upon the volume flow rate 'Q', the valve opening or position 'l' , the valve diameter 'D', the upstream
pressure' 1P ', the pressure drop across the valve ' P ',
the viscosity of the fluid ' ', and mass density ' '. By
applying the Buckingham’s -theorem, a
dimensionless expression for the flow force acting onthe valve stem may be obtained as follows,
)D/(PD
Qf
DP
F32
1
(3)
where2
1 DP
Fis defined as the dimensionless exciting
force dF and )D/(PD
Q3
is defined as the
dimensionless volume flow rate dQ . The experimental
results shown in Fig.4 show the variation of the
dimensionless exciting force with the dimensionless
volume flow rate. The test runs were made at highReynolds numbers and turbulent flow at different flow
rates and pressure drops. The dimensionless force ' dF '
and the dimensionless volume flow rates were
calculated as the average of the test runs at a constantvalve position. The results show that the dimensionless
exciting force decreases as the valve opening increases,
see Fig.5. For small valve opening values, a littlechange in the plug position yields to a significant
variation in the value of the exciting force whichmeans that the effectiveness of valve position becomes
very much pronounced for small values of valveopening. Based on the experimental results an
approximating equation may be obtained as follows,
41356.1Qlog109049.0F dd (4)
Formula (4) was established with the least-square-error technique of fit using the experimental data, and
automated curve fitting software.
Fig. 4. The variation of the dimensionless exciting
force with the dimensionless volume flow rate
V. Experimental Uncertainty
Experimental uncertainty in the present work has
several sources. The most obvious and easiest toquantify is the error associated with the
instrumentation. This includes the pressure transducers,the orifice flow meter, and load cell. The uncertainty
for pressure measurements was 1.0 percent. The
flow meter had an error of one percent of the reading.
The load cell had an error of 5.0 percent. Other
sources of error in the study included the plug percentopening and the errors caused by plug centering. The plug percent opening error was investigated
experimentally using repeated measurements and
applying statistical arguments. The measurements weretaken using a dial indicator that gave an error of one
percent of the valve percent opening. The uncertainty
associated with plug percent opening error wasnegligibly small. Centering the plug with equally
spaced was investigated. This was verifiedexperimentally by rotating the valve stem after the
setting of the valve opening, while takingmeasurements in the load cell. The results showed that
the flow force acting on the plug (valve stem) couldvary by a maximum of 4 percent depending on the
valve opening percentage and the plug's rotation. The
experimental uncertainty changed with valve opening.
When calculated as a percent of the measured vC , the
experimental uncertainty ranged from a minimumvalue of 1.66 percent error to a maximum value of 7.21
percent error.
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VI. Computational Fluid Dynamics (CFD)
Using FLUENT 6.3, a three dimensional model of the valve body and connecting pipes shown in Fig.6 is
created to investigate the flow. The valve was modeledwith the plug positioned at different percent openings.
The converged flow field was used with Equation (1)
to calculate the valve vC . Also, the converged pressure
was used to calculate the flow net force acting on the
valve stem.
Geometry: The fully dimensioned valve was modeledand the plug and seat region was well represented.
Upstream of the seat, the inlet pipe length divided by
the valve diameter
D
Lwas 5, and downstream of the
seat, the outlet pipe length divided by the valve
diameter was 11.
Grid: The grid used in the numerical study was made
up of tetrahedral cells, the nodes of grid were clusteredin the plug and a seat region since this was the area of
largest flow gradients. In addition, an effort was madeto reduce the grid distortion. Fig 5-a shows an extendedview of the grid and Fig.5-b shows the expanded view
of the grid.
Boundary conditions: All solid boundaries wererepresented as walls with no slip velocity conditions
and log well turbulence conditions. Inlet conditionswere represented by a uniform total pressure. The
treatment of pressure inlet boundary condition can bedescribed as a loss-free transition from stagnation
conditions to the inlet conditions. For incompressibleflows, this is accomplished by application of the
Bernoulli equation at the inlet boundary. The outlet
boundary conditions were set as a uniform static
pressure. The boundary conditions at inlet and outletsections of the domain of solution were obtained fromthe laboratory experiments. Turbulence intensity and
turbulence length scale at the entrance cross section
were set as 81eR 16.0I and hd0175.0L [13],
where hd is the hydraulic diameter. Test cases were
run with 10 and 20 percent turbulence intensity, nosignificant change in the predictions was observed.
Selection of turbulence model: The choice of turbulent model depends on consideration such as the
physics encompassed in the flow, the established practice for a specific class of problem, the level of
accuracy required, the available computational
resources, and the time available for the simulation.Two equation turbulence models have become the
most popular, since they are relatively simple to program and place much lower requirements on
computer resources than other more complex models
(Algebraic and Reynolds stress models). The k
model relates the turbulence viscosity, )sPa(t , the
turbulence kinetic energy, )sm(k 22 , and the
turbulence dissipation rate, )sm( 32 . The k
turbulence model is similar to the low Reynolds
number k model, with replacing , which
represents the specific dissipation rate )s( 1 .
Researchers have developed many turbulence models
provided results with major differences andcontradictions in some cases. The model used in this
study was the two-equation k model. The Standard,
RNG, and Realizable k models are investigated.
Other turbulence models (Standard and Shear Stress
Transport, SST k ) were used in an attempt to
obtain the best convenient model for the present study.
All turbulence models were used with the standard parameters.
Numerical accuracy: All conservation equations are
discretized in FLUENT using a finite volumeformulation with second order spatial accuracy. Thecontinuity is satisfied using a SIMPLE (semi-implicit
pressure linked equations) algorithm. Normalized
residuals were used for the convergence criteria, which
was set at three orders of magnitude.
The numerically tested valve was geometricallysimilar to that applied in the experimental
investigations. It was assumed that the flow is three-dimensional, steady, isothermal, turbulent, Newtonian
and incompressible. However, body forces have beenneglected. Water, at the room temperature, was applied
as the fluid passing through the valve. The flow wasgoverned by the system of mass and momentumconservation equations. In turbulent flow region the
system of equations RANS (Reynolds Averaged
Navier-Stokes equations) was closed by theintroduction of the turbulence model.
Fig. 5. Generated mesh for investigated geometry
(a) Extended view
(b) Close up view of grid
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VII. Results and Discussions
The flow field was examined through theinterpretation of the post process data resulting from
the model solution. The results of the numerical studyare shown in Fig.6 through 11, and Fig.13 shows the
comparison of numerical and experimental results of the inherent valve characteristics.
Flow field: The numerically obtained path line patternsin a partially opened valve on the longitudinal mid
plane for 5, 10, 20, 30 and 40 percent openings are
illustrated in Fig.6. On the upstream surface of the plugdisk a stagnation region forms and outside of this
region, the flow direction is towards the edge of the
disk. In each case, the flow initially accelerates throughthe plug and seat region and then flows downstream in
the form of a wall jet at the side of the valve body, andat the open valve side. For valve opening up to
approximately 30%, flow separation from the plug witha second recirculation zone occurs between the wall jet
and the plug surface. At valve opening greater than30%, the results show that the flow remaining attached
to the plug surface, Fig.6-e. In addition, a largerecirculation region develops on the downstream sideof the plug at the closed valve body. As the valve
opening increases, flow separation from the valve body
with a recirculation zone between the jet and valve body at outlet path of the flow occurs. A vena contracta
phenomenon and a hydrodynamic minimum flow areadown stream of the plug are observed. The jet flows
interact and mix downstream of the trim area andsufficiently far from it the flow again occupies the
available flow area and approaches a fully developed pipe flow.
Pressure contours: Fig.7 displays the numerically
modeled contours of the static pressure in a plane
placed close to the upstream surface of the plug. Atsmall opening value, the results show that the pressurecontours are radial relative to valve centerline, which
implies that the pressure field is primarily one
dimensional with the axial (stem) direction. As thevalve percent opening increases, the static pressure
contours become two dimensional and the gradients areless confined to the gap between the plug and seat. In
each case, the pressure decreases in the downstreamdirection with the largest pressure gradients occurring
in the plug and seat region. No significant pressurechanges are observed upstream of the seat and onlyminor changes are observed downstream of the seat.
Fig.8 shows the variation of the static pressure along a
line in a longitudinal mid-plane placed close toupstream surface of the plug. The pressure has a
maximum value corresponding to zero total velocity at
stagnant point, see Fig.9. At the plug edge the static
pressure has a minimum value while the velocity of thefluid has a maximum value.
Fig. 6. Numerically obtained path line patterns
in a partially open valve.
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(a)
(b)
(c)
Fig. 7. Pressure contours at upstream plug surface.
(a) 5% opening
(b) 20% opening
(c) 40% opening
(a)
(b)
(c)
Fig. 8. Pressure distributions at upstream plug surface
(a) 5% opening
(b) 20% opening
(c) 40% opening
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(a)
(b)
(c)
Fig. 9. Velocity distributions at upstream plugsurface.
(a) 5% opening , (b) 20% opening
(c) 40% opening
Fig. 11. Comparison of flow forces for different
turbulent models.
(a)
(b)
(c)
Fig. 10. Turbulent Kinetic Energy contours.( K-ω Turbulence Model.)
(a) 5% opening, (b) 20 % opening
(c) 40% opening
Fig. 12. Comparison between experimental an
theoretical (CFD) values of flow force.
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Turbulent kinetic energy: The constant contours for
turbulence energy are shown in Fig.10. The separatedregions of the flow where shear layers exist have the
highest magnitudes of the turbulence kinetic energy 'k'.
The magnitude of the turbulence kinetic energy in the plug and seat region of the valve is high, this is due to
creation of large shear layer as the flow is squeezedthrough this region.
Exciting force: The fluid flow forces acting on the
valve stem were obtained using different turbulentmodels, as shown in Fig.11. It was noticed that no odd
discrepancy neither in the pattern nor the values of theflow forces, for all investigated openings. Moreover,
the flow forces, computed by the k (SST) model
for different valve's openings (5-40 %), have the less
percent of deviation with experimental results,compared with other turbulent models. Fig.12 shows
the comparison between the experimental results andthe numerical results. The maximum percentage of
deviation was 12.81% at 40% valve opening.
VII. Conclusions
Under completion of the study, the followingconclusions are withdrawn,
1- The flow field was examined and the results showthat the valve geometry has a significant impact on
the turbulent flow passing through the valve. The
results are in good agreement with those obtained
by many researchers as pointed in [7] and [15].2- Under the partial opening (greater than 5 %)
condition, a complex three-dimensional (3D) flow
structure set up in the valve region leading to high pressure variations in the valve trim region.
3- The fluid flow forces that acting on the plug and
stem depends on the valve opening percentage. It
was found that the smaller valve opening, the larger the exciting force acting on the valve stem. Theharmful effect of the fluid flow forces (exciting
forces) is very much pronounced at relativelysmaller valve opening.
4- The simulation results for turbulent flow with
k model were more accurate than the k
model. Moreover, k model was simpler and
faster in convergence than the k model. These
results are in agreement with those obtained by [10].
References
[1] Miller,H.,1998, "Control Valve Applications", Chapter12,
Control Valves: Practical Guides for Measurement and control.G.Bordon, Editor, ISA Press, Research Triangle, North
Carolina
[2] Miller H., and Stratton L., 1997, " Fluid Kinetic Enrgy as a
Selecti on Criteri a for Control Valves", ASME Fluids
Engineering Division Summer Meeting.
[3] Hardin J., Kushner F. and Koester F., 2003, "Elimination of
Flow-Induced Instability From Steam Turbine ControlValves", Proceeding of the Thirty-Two Turbomachinery
Symposium.
[4] Wojtkowiak J., and Oleśkowicz-Popiel C,.2006,"Investi gations
of Butterlfly Control Valve Characteristics", Foundations of
Civil and Environmental Engineering, V.7, ISSN 1642-9303
[5] Kim R. H., and Huang C., 1993, "3-D Analysis Butterfly
Valve Fluid Flow", Proceeding of the Korean Fluent User's
Group Meeting, Seoul, pp 43-57.
[6] Chern M., and Wang C., 2004, " Control of Volumetric Flow-
Rate of Ball Valve Using V-Port", Trans ASME J. of Fluids
Engineering, Vol. 126, pp: 471-481.
[7] Davis J., and Stewart M., 2002," Predic ting Control Valve
Performance-Part I: CFD Modeling", Trans ASME J. of Fluids
Engineering, Vol. 124, pp: 772-777.[8] Hong G., Xin F., and Huayong Y., 2000, "Numerical
Simulation Of Cavitating Flow In Hydraulic Conical Valve" ,
A project supported by SRF for ROCS, SEM and National Natural Science Foundation of China (59835160).
[9] Amirante R., Del Vescovo G., and Lippolis A., 2006, "
Evaluation of the Flow Forces on an open Center DirectionalControl Valve by means of a Computational Fluid Dynamic
Analysis", Journal of Energy Conservation & Management,
Vol. 47,pp:1748-1760.
[10] Oza, A., Ghosh, S., and Chowdhury, K.,2007," CFD Modelingof Globe Valves for Oxygen Application", Proceeding of the
16th Australasian Fluid Mechanics Conference.
[11] Au-Yang MK, Jordan KB, Nucl Eng Dec.1980,"Dynamic pressure inside a PWR-a study based on laboratory and field
test data", Vol. 58, pp:113-125.
[12] Research Triangle Park, North Carolina: Instrument Society of America., ISA-S75.01-1997, "Control Valve Sizing
Equations",
[13] Fluent 6.3 User's Guide, Fluent Inc. 2005.
[14] Launder B. E. and Spalding D. B., 1972,"Mathematical
Models of Turbulence", London, Academic Press.
[15] Bernard, S., Muntean, S., Susan-Resiga, R. and Anton, L.,
2005, " Vorticity in Hydraulic Power Equipment", Proceedings
of the Workshop on Vortex Dominated Flows, Achievements
and Open Problems, Timisora-Romania.
Acknowledgements
The authors want to express their great thanks and sincere gratitude
for both Prof. Zakria Ghoneim (Mechanical Engineering Department,
Faculty of Engineering, Ain Shams University) and Prof. El-Sayed
Saber (Mechanical Engineering Department, College of Engineering,
AASTMT) for their continuous guidance and help during theexecution of the present research work.
Authors’ information 1Amr Hassan was birthed on 21-07-1966. A
master degree in mechanical engineering was
obtained in 1994 from faculty of engineering,Alexandria University – Egypt. A PhD was
obtained in 2002 from School of Mechanical,
Materials, Manufacturing Engineering andManagement, University of Nottingham,
Nottingham, UK.
He conducted previous research studies in the fields of windshield
defrosting and demisting in automotive. He is now interested in the
using computational fluid dynamics in flow simulation.
Dr. Amr is member of Society of Automotive Engineers, SAE and
IMarEST (The Institute of Marine Engineering, Science and
Technology)
2Ashraf Sharara was birthed on 05-01-1970.
A master degree in mechanical engineering
was obtained in 1997 from faculty of
engineering, Alexandria University – Egypt.
Currently , a PhD student at faculty of
engineering, Ain Shams University – Egypt.
He conducted previous research studies in the fields of applied
mechanics. He is now interested in studying the phenomenon of flow
induced vibration in fluid valves.