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RSITAT HAMBUR
TEHIU8HE UNIVERSITEITLsboradwn voor
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015- IIIVS 015. 781836CAVITATION AND ITS INFLUENCE ON INDUCED
HULL PRESSURE AMPLITUDES
-RECENT RESEARCH AT
THEINSTITUT FÜR
CAVITATION AND ITS INFLUENCE ON
INDUCED HULL PRESSURE AMPLITUDES
-Recent Research at che
Institut für Schiffbau
derUniversität Hamburg
by
E.-A, WEITENDORF
Hamburg University / Hamburg Model Tank
Bib;ofheek van de
Sche?pvartkun
le h
H
E? DLeft
t;
- i o
DATUM:Abstract
Introduction
Measurements and Calculations of Propeller-excited
Pressure-Amplitudes
Measurements and Calculations of the Pressure
?iels on Propeller Slaes
4
Influence of Undissolved
Air Content
on Cavitation
Phenomena at the Propeller Blades
and ori Inducediull Pressure Amplitudes
Theoretical Research
on Cavitation Inception
with Application of Bubble Dynamics
Conclusion
References
Figures
Contents
ha
ArchiefNek&weg 2, 2628 cl)
Deifti
Ab st ra c t
A critical review of the
following subjects is given:
Measurement _adcacujatipQ of
Propeller
excited
Pressure-Ampli-tudes.
It was found that in the case of heavily cavitating frigate
pro-pellers a decrease of the pressure amplitudes occurs in front
of
and directly above the
propeller compared with
noncavitating
condit-ions. Behind the propeller
plane the cavitating tip
vortx with
nooes having a mean diameter of
about 3 to 5 per cent of
the screw
diameter amplifies the
pressure impulses. By means of
theoretical
and experimental investigations it could be proved
that the wave
length (i.e. distance
between two nodes) of the
cavitating tip
vortex causes amplitudes of
discrete frequencies. The
wave length
itsSelf depends on the meandiameterof
the cavitating vortex
and the
cavitation number. If the wave lenght x attains
a value
corres-ponding to the number of
propeller blades e.g.
= 1200 for a three
bladed propeller, the
amplitudes of the blade frequency will be
amplified. Analog effects will
happen at twice the blade
frequency
with a wave length of
=60°.
Measurement and Çcylton_of
the Pressure _Fields
on Propeller
Blades.
The measurement of the
instationary pressures at 235 points
on the
blades of a 1.40
m model propeller were
executed in a ship-like
wake
in a wind tunnel at Göttingen. The results of these
measurements at
Göttingen are compared
with the results of
an instationary lifting
surface theory. For
one case they agree
very well, but from
real
pressure distribution of the propeller investigated.
3. Influence of Undissolved Air Content
on Cavitation Phenomena at
the Pro_pelTer Blades and on nuced_HilJ Pressure
Amplitudes.
This investigation consisted of the
application of the Scatterad Light Technique for measuring the undissolved
air conteìt of a
cavi-tation tunnel and
simultaneous measurements of propeller-excited pressure amplitudes on a flat plate above
the propeller.
The main results of the measurements
are:
Increasing relative free gas volume for cavitation
tests and
higher revolutions of the model
propeller in a wake causes earlier inception and
increase in the size of the cavity and
tnerefore increasing nondimensional
pressure amplitudes. Cavitation tests for estimating the propeller-excited
pressure amplitudes should include the simultaneous
determination of the relative free gas content and later on its possible
con-trol
4. Theoretical Research
on
of Bubble Dynamics.
The theoretical research on this
subject uses as input the nuclei
distribution measured in the above
mentioned point 3. Not only the pressure field for a two phase flow around
a hydrofoil is
cal-culated but also the growth of single
bubbles in this pressure
field. The result
greater number of smaller bubbles with a diameter less than
lO,Mm have an important influence on the cavitation phenomena, if
the
1. Introduction
The paper presented here gives a review of propeller and cavi-tation research con ducted at the Institut für Schiffbau of the Hamburg University within the Special Research Pool "Schiffs-technik und Schiffbau" (SFB 98) during the last four years.
Since there were several activities in this field, it is impossible to describe them all in detail. That is feasible only for those topics which are directly implied by the title. Others an only be mentioned by way of suggestion in this introduction.
For instance Laudan ti] has complemented the Wageningen
"four-quadrant" measurements of propellers f2) in open water. He per-formed the "four quadrant" propeller measurements in a quasi-steady manner using four typical ship models in front of the propellers.
In this way global statements about the wake fraction and thrust deduction fraction were found: the wake fraction remains constant from the condition of operation to the reversing point, afterwards decreasing to zero. On the other hand the thrust deduction fraction diminishes in a linear way from the point of operation to a
nega-tive value.
In an additional investigation Laudan (3] measured the influence of the cavitation on the propeller-forces occuring during crash stops on straight courses. The measurements were performed in a
cavitation tunnel in a quasi steady way. For the propellers used here it was shewn that the influence of the cavitation was not excessive. But at least the result was that the stopping time was prolonged by 20 per cent and the stopping distance was increased by 15 per cent.
Furthermore this project "Safety against collision" of the SFB 98
investigated the influence of oblique flow on the propeller having different advance angles
{43
and made threedimensionalwake measure-ments during oblique towing of the ship model
[57.
But now results are to be presented,whose origin
concerns the author directly.
2. Measurement and Calculation of Propeller-excited Pressure
iplitudes
2.1. Measurements of Pressure Arn2uitudes for heavil,
cavitatinS
fr19
292!1
In order to study the influence of cavitation on the blade fre-quency pressures for heavily cavitating
frigate propellers of different design, measurements with seven
pressure pick-ups on a,
flate plate (Fig. 1) were carried Out in the medium sized cavitation
F. I
tunnel of the Hamburg Model Basin (HSVA). These investigations
E6]
contain numereous results with a wide variation of the main
para-meters of these three, four - and five bladed propellers
valid for homogeneous but also for inhomogeneous flow, can be
found in Fig. 2.
Here the nondimensional pressure amplitude
K z
p3
Ap
n D
is plotted against the coordinate in flow direction x/R. The figure concerns homogeneous flow. The upper diagram stands for a
propeller (HSVA-Propeller 1240), whose maximal circulation or
loa-ding is drawn to inner radii, the lower stands for an optimal pro-peller (HSVA-Propro-peller 1283). Both propro-pellers possess three blades. Parameter of the curves is the cavitation number
VA I
4A
p - VA2In this definition VA means the speed of advances of the propeller. The solid curves are valid for the cavitation free condition of the propeller, i.e. there was an open connection between the test section of the tunnel and the atmosphere. The procedure of the tests was that the pressure in the tunnel was reduced step by step. So
the cavitation numbers,given in the legend of the figure, were reached. For the optimal propeller the following result for the cavitating condition was found:
In front of and directly above the propeller plane a decrease of the pressure amplitude occurs when compared with the cavitation-free condition. The decrease of the pressure amplitude by cavitation
i
can be explained in the following manner:
The propeller excited pressure amplitude is caused by two influ-ences, i.e. the thickness and the loading of the blade. Since in case of heavy cavitation the thrust breaks down, the loading
in-fluence can be reduced more than the thickness inin-fluence will
in-crease from cavitation. The smaller dein-crease of the amplitudes for the "noiseless" propeller in the upper diagram is due to the greater cavitation-free area of this propeller.
Behind the plane of propeller 1283 the increase of the amplitudes, compared with the cavitation free condition (ATM),
is caused by the cavitating tip vortex. Already
by observing the stroboscopic photographs of both propellers in
Fig.3 the influence of the
cavitating tip vortex on the pressure amplitudes can be detected: The optimal propeller 1283 possesses a thick tip vortex and
accord-ingl,y in Fig. 2 an increase of the amplitudes. On the contrary
the noise-less propeller 1240 shows very little of a cavitating tip vortex in Fig. 3 and correspondingly
no amplification of the amplitudes behind the propeller plane in Fig. 2. In order to avoid misunderstanding at the end of this chapter, it must be stressed that this practice of unloading the propeller
ip can only be applied for propellers in wake fields of fast ships, mainly navy
-
6-2.2. InvestiSations of the Cavitatin Tip Vortex with nodes
Looking more precisely in Fig. 4 at some cavitating tip vortices in homogeneous flow, the following can be discovered:
At constant advance coefficient, bu4iecreasing cavitation number
VA the cavitating tip vortex becomes more and more thick.
Finally this vortex shows nodes at regular intervals which are marked by arrows in the photographs of Fig. 4. These notes are
stationary with respect to the running propeller. The poitions of the nodes are determined by the mean radius of the tip vortex and by the cavitation number
dVA. This was, already shown 1930 by
Ackeret [7J . Turning with the propeller, this cavitating tip vortex contracted at different positions causes pressure amplitudes of discrete frequencies, depending on the wave length of the vortex,
i.e. the distance between two nodes.
In the theoretical investigations {8J of this physical phenomenon the pressure impulses,created by the cavitating tip vortex, were regarded as an effect of displacement. This was simulated by suitable source-sink-distributions, arranged on the spiral line described by the propeller tip in operation. Now it is imaginable that the pressure amplitude, created by the displacement of a body, is proportional to the variation of the cross-section of this body,
namely
K
dx)
if z. is the circumferential coordinate.
In the calculations the
Fcx
(R
9sin2(xr))
'1
R
R0 Xø/
(-x
J
is built up of two parts: the round bracket
stands for the
wave-like and cavitati.ng hollow vortex (sketch No. 1), and
the square
yort
bracket for the ellipsoidal hollowYThe
designations in the round
bracket for the wave-like hollow vortex are:
= tne nican radius of the
cavitating tip vortex,
nD
Ram
= amplitude of the cross-section of the tipvortex,
to be taken from photographs,
=
wave length of the hollow vortex in the theory by Ackeret [7],
R.,
Çkefci/o'i
R Kç
NRiRa
K1 z = a = 1 4 (2.2) VAthe propeller blade,
coefficient,
number of blades,
inner and outer radius of
= thrust
Qfl
D4 V.A = advance coefficient,R0,
ir
(2.1)m
- circumferential coordinate
The designations in the square bracket for the ellipsoidal hollow
vQ'rtL)( (scetci No2
are:kefcb W04
A initial value of the hollow vortex,
s
final value of the hollow vortex,
m parameter of inclination.
The cross-sections applied in the theoretical investigations correspond to formula (2.1). Some examples
of cavitating tip vortices used in the calculations are shown in Fig. 5.
9
In the calculations the value - O
lies at
the position
of
the lifting line vortex ofthe propeller blade,
i.e. trie 1/4 - point of the propeller profile. The different
in-fluences of the shape parameters in formula (2.1), namely
Rk the mean radius of the cavitating tip vortex,
Ram
a the amplitudeof
the cross-section of the tip
vortex,
a the wave length, the mitai value, the phase angle,
m = the parameter of inclination,
were investigated in a computer program. In order to enable
com-parisons with the present measurements [6] ,
the computer program contains all contributions of the propeller excited pressure am-plitudes, namely the influence of the loading
of
the blades,
in-cluding the steady cavitation, the influence of the thickness
of
the blades and the influence of the wave-like cavitating tip vortex with its effect of displacement. In the detailed report
8) all
re-sults of these calculations are given. But here the results of the variation of the wave length only can be shown in
This figure contains two diagrams, the upper results are valid for the third harmonic order of the pressure fluctuations (blade frequency) and the lower for twice the blade frequency. The non-dimensional pressure amplitudes K3 and K6 are plotted against the flow direction x/R4. Behind the propeller plane in the region
> 1.0 the normal contribution of the propeller, i.e. thick-ness and loading effects of the blades have vanished. This is the reason for showing the results up to x/R = 2.0. Parameter of the different curves in Fig. 6 is the wave length x0.If the
wave length x attains the value = = 1200 for N = 3, then the
third harmonic of the pressure will be the strongest amplitude. If the wave length
x
is equal 60°, twice the bladefrequency will
be thgreatest. This can clearly be found in Fig. 6. The oscillat-ions of different curves in Fig. 6 are due to the wave length. Since these contracted tip vortices leaving the different blades are stationary with the positionsof their nodes with respect to the propeller, all respective nodes of different blades must be in one plane. This plan is located parallel to the propeller plane. The distances between two such planes, corresponding to the oscillation ir Fig. 6, are equal to the value x/R = X =
X0.
As the theory by Ackeret
[73
shows, the wave lengthx depends on
the mean radius 0f the cavitating hollow vortex. In the present
investigation
[83
this statement was also confirmed for the spiralcurved tip vortex of a propeller. Ackeret's result namely was valid for a straight hollow vortex. The mean radius of the cavitating tip vortex depends on the cavitation number, the propeller loading and is inversely proportional to the blade
u
-in formula (2.2). In this way all dependencies not only for the
t
wave length x0 but also forean diameter of the cavitating tip
vortex are formulated. But the merely theoretical calculation of the pressure amplitudes of a cavitating tip vortex with nodes is not feasible, for the position of the first node, the initial and final value of the vortex and its shape amplitude
Rkam can only be
ob-tained from measurements. From photograph of corresponding tests these value are gathered. The valuesare used for the calculations whose results are shown in Fig. 7.
For the purpose of comparison the results of the measurements are given additionally, obtained with the five pressure pick-ups located along the direction of flow (see Fig. 1). In Fig. 7 results of calculations and measurements for J 0.72 up to the 9th
har-monic order are given for the cavitation numbers
p-pv
-2.0, 1.75, 1.50, 1.25 and 1.14.
VA
-
-Comparing the results of calculations and measurements, a quite satisfactory agreement can be found, especially for = 1.75. For this case an exellent agreement occurs, above all
at the
position p 4 and P5, where the
cavitating tip vortex is of do-ininating influence. For this case not only photographs but also
coloured slides were available. These were used for determining the shape parameters of the vortex needed for the calculations. Here one can see, how important the accurate determination of the shape parameters is. Only if the input values of the computer program conform to reality, an agreement between measurement and calculation can be obtained.
In order to avoid the drawback of every time having to take
photographs for the input data of the computer program, empirical formulas for the shape parameters of the tip vortex were
develop-ed . By means of these emperical
formulas, it seems possible to compute approximately the pressure fluctuations caused by cavitating tip vortices without having to take photographs. At the er1d of this chapter the following
13
-the influence of -the cavitating tip vortex with nodes shall be
given:
Not only by measurements but also by calculation
it was proved
that the cavitating tip vortex with nodes, having a mean diameter of about 4 per cent of the propeller diameter,
causes greater am-plitudes of higher blade frequencies. These can be observed in full
scale and model
measurements. The phenomenon of these nodes occurs
in a ship wake too.
An additional aim should be the calculation of the cavitating
tip
vortex with nodes in a ship wake. Preliminary
calculation of this problem are already carried out for single
screw container ships using the above mentioned
computer program in a quasi steady manner for different loadings
of the propeller in the wake. The result was that the pressure amplitude excited by the cavitating vortex was of minor magnetude
compared with the other con-tributions of the propeller. A concluding
statement about the influence of the cavitating tip vortex with
nodes in a wake can
only be drawn after having performed extensive theoretical
in-stationary calculations. It is imaginable
that the instationary variation of the shape of the cavitating
tip vortex in the wake
may generate pressure amplitudes of the same magnitude as the other exitations of the propeller.
3. Measurement and Calculation of the Pressure
Fields on Pro2elier
Blades
Concerning a realistic
the propeller, the
inflow condition at the stern as well as the pressure distribution on the pressure and
suction side of the blades is needed.
Regarding the pressures on the propeller, auxiliary means consist of calculations of the unsteady
lifting
surface theory and measurements. In cooperation
between the In-stitut für Schiffbau Hamburg (Special
Research Pool 98) and the Aerodynamische Versuchsanstalt (AVA) in Gottingen measurements of the pressure
distributions on both side of a model
prpeller
were carried out in a wind tunnel with
a cross-section of g m2 (10, 113. The tests were
performed in a ship like wake flow. On the 4 blades of the 1,4 meter wide model 235 orifices
were
distributed, mostly concentrated at the leading edges and
the
outer radii. The measurements
were performed by means of the so called "indirect
method", i.e. the 235 orifices were connected to one pressure
pick-up using five scanning valves. In
this way
'n
a calibration of plitude and phase
was necessary for each orifice. In the figures 8 to 10 for instance,
results of the measured
pressure distributions for the radii r/Ra - 0.50, 0.90 and 0,975 are shown. Here the nondimensional pressure coefficient
p po
cpb)
QW2
2R
is plotted against the relative position along the chordlength
xii (x . distance from leading edge, i chord length).
X/
With the exception of the blade tip (see Fig. 10),the influenceof the inhomogeneous inflow (ship wake) is concentrated on the fore part of the chord, i.e. x/i 0.5. The influence becomes dominant at the leading edge. The lowest pressure, giving a
pressure coefficient c = -0,362 at the blade position y = 30° ra
at chord station xii = 0.007, was found on the radius r/Ra = 0.80. The influence of the tip vortex can be seen in Fig. 10 for the suction side. The great pressure &ifferences between pressure and suction side at the trailing edge indicate the threedimens-ionai flow around the blade tip, being typical for the tip vortex
roiling up.
The choice of air as fluid medium has the advantage that no cavitation can occur. The eperimental parameters were such that the flow remained incompressible so that the incompressible lifting surface theory could be applied for the calculations. Hence suitab1e possibility for the comparison between the re-sults from theory and measurements is available. Furthermore,
by using such a big model of 1.4 meter diajneter, the orifices
for the measurements could be placed very near to the leading edge. On the other hand, a drawback of using air as the fluid
17
-medium was the lower density of air compared with water. This leads to smaller pressure difference between suction and pressure side, approximately 0.025 bar. Above all, using the "indirect method" of pressure testing, these small pressure differences could only be obtained with a lowered accuracy. To some extent, the determination of the zero level for the pressure coefficient gave rise to certain difficulties, which only could be overcome by most precise measurements of the atmospheric pressure during the repeat tests. All in all, the AVA in Göttingen estimates the error of the whole measurement at 5 per cent with respect to the experi ence with other measuring techniques. This value
of ± 5 per cent seerr6 to be pretty good. Here it cannot be
de-cided whether the pressure differences at the leading edge could be measured with the necessary accuracy considering the ine-vitable inaccuracies of manufacturing in the profiles of the model propeller. This is the occcasion to give the hint that the AVA in Göttingen at this moment is pursuing the fundamental problem of measuring pressure differences on foils of rotating systems. The result of this investigation may give an additional insight into the accuracy of the propeller measuremnt reported here. Nevertheless this propeller measurement leads to the
possibility of comparing the results of lifting surface theories. For this reason these wind tunnel tests were ordered by the
Special Research Pool (SF8 98), in order to compare the results of a computer program [12] based on the lifting surface theory [13) developed at the Institut für Schiffbau of the Hamburg
University.
In Fig. 11 and 12a comparison is
19
-results from AVA [111 and the -results of the Hamburg calculation E123 for the position 00 (12 o'clock position) and - 3300
(starboard) at the radius r/R = 0.90. For this case the agreement between computation and test seems pretty good. But using the same computer program for the HSVA-propeller 1917 leads to a substantially different picture in Fig. 13. For both the blade
positions
°0
-
00 and) 330° (starboard) the cavity lengths
at the radius r/R - 0.90 for the cavitation number
p - p
C
= z 0.211n
,2 (nD)2
are shown. In the calculation the vapour pressure, corresponding
to = 0.211, is only obtained for ten per cent of the chord length, whereas the real cavity lenght of a corresponding
cavitation test is extended over 55 per cent of the chord length
(see Fig. 18, upper row). This suggests that the mere application
of the cavitation number of the prototype is insufficient. It could be important to take into consideration the dynamics of the cavitating gas bubbles additionally.
Corresponding to the blade position = 330° in Fig.13, the vapour pressure corresponding 0.211, which is approximately necessary for the cavitation inception, is not attained in the calculations. This statement gives rise to the assumption that the pressure distribution of the computer program [123 does not fit the real values of the propeller pressures of a cavitation
test.
21
-to compute the circulation distribution of the HSVA propeller 1917 in an axial model wake. This circulation can be used for the cal-culation of the blade frequency pressure without cavitation on a
flate plate
[83.
The result is shown in Fig. 14. Againthe
the-oretical values do not match the measurements. Once more the suspicion rises that the computer program f123 gives too small pressure differences between pressure and suction side compared with the reality. On the other hand, it must be admitted that the calculated blade frequency pressures on a flate plate do not indicate whether the calculated pressure differences on the
blades are right or wrong. For instance, computations of the
pressure differences on the blades of the HSVA-propeller 1917
Hamburg
ordered by the Institut fUr SchiffbaJ'?rom
another institute gave unsatisfactory results, inspite of better agreement of the
simutaneously calculated calculated blade frequency pressures on a flat plate with the measurements in Fig. 14.
Concerning the calculations of the pressure differences on the propeller blades in a ship wake by means of the lifting surface theory, it would be of utmost interest to see what the comparison of different lifting surface theories proposed by the ITTC would look like. Beside the AVA-model propeller the HSVA-propeller
1917
(Zeise-design) would offer a suitable object for purposes of
at the ProEeller Blades and on Induced Hull Pressure Am2litudes In a paper on propeller-excited hull forces given in 1972 by
van Oossanen and van der Kooy 14J, it was evident that for equal nondimensional flow conditions but different absolute revolutions (i.e. n = 20 and n = 30 Hz),the nondimensional
propeller-excited pressure amplitudes were different. That means an uncertainty with respect to the evaluation of the vibratory behavior of a ship.
Two possible influences concerning these differences were taken
into account:
the influence of the neglected Froude law of similarity and the free air content of the tunnel water.
Using the Froude law of similarity, the correct pressure distribution on the propeller blades in radial direction is guaranteed. But normally the revolution based on the Froude number can not be realized, because it is out of the range of a normal cavitation tunnel.
With respect to the free air content, this content of the tunne' water, i.e. the free gas bubbles of test water, governs the cavitation inception.
Taking the above mentioned influences into account as much as possible, new tests were performed in the medium sized cavitation tunnel of the Hamburg Model Basin in November and December of 1974. The axial component of the flow field in the propeller plane
23
-was simulated by grids of varying density.
Three kinds of measurements were executed simultaneously:
Measurement of the undissoived air content by the laser light
scattering method.
Measurement of the propeller-excited pressure amplitudes on a fiat plate above the propeller.
Stereometric photography of the extension of the cavitation on the propeller blades.
In this lecture a short review of the above mentioned measure-ments under number 1) and 2) shall be given. A more detailed description of these measurements was given in the IfS-Report
312 A [15).
The scattered light technique was applied in close cooperation with A. Keller of the Technical University Munich. He developed this method up to practical application of cavitation
tests [16].
(F
.1),
In our case of applRà Tàthe optical control volume defined
by the cross-sectional dimensions of the light beam and the optics of the system detecting the scattered light had a cross-section of 1.2 m2. The control volume was located in front of the propeller plane. Directly behind the control volume, the flow velocity
was
measured by a Prandtl tube. The flow velocity is required for the estimation of nuclei concentration of the fluid. The
ca-libration of the photomultiplier used as the scattered light detector was performed with latex spheres of known diameter. These were injected into the control volume. The electrical
output pulses of the photomul tipi ier which are proportional to
the "nucleus size were evaluated by an HP-computer in an on-line mode. Thereby, it was possible to print a nucleus size histogram immediately after each test.
For the example of degassed water, a histogram is shown in Fig. 16. The abscissa is the size o the bubbles measured in the range
between 20 and 350 microns.
The recommendation of the ITTC Cavitation Committee, taken
into consideration in this case, is the following that the nuclei size should be measured from 10 to 250 microns in diameter.The dashed line in Fig. 16 is the size histogram. Additionally, the diagram contains the fraction of the relative free gas
volume
d
per bubble range (full line). The relative free gas volumec& is the ratio of all measured gas bubbles per volumeunit to the volume unit of the fluid. As mentoned, the full line represents the fraction of all measured relative free gas volumes per bubble range, i.e. between 20 and 69,6 microns. Summing up all the fractions of the relative free gas volumes per range,
we obtain the total measured relative free gas volume, i.e.
c= 0.118 x 10 in the figure.
By gassing and degassing, it was possible to vary the free air content of the test water in a rather wide range. For the case of gassed water, the respective figure like Fig. 16 contains
a greater number of bubbles and greater relative free gas volume. After and before each test series the total air content c0 was determined by a van-Slyke-apparatus.
25
-As mentioned before the propeller-excited pressure amplitudes were measured on a flat plate above the propeller. The sketch of
the test setup and positions of pressure pickups were shown in Fig. 1. The first tests of the heavely cavitating frigate propeller (HSVA-propeller 1283) with open water conditions were performed without artificially changing the free gas
con-tent of the tunnel water. The purpose of this procedure was to find the connection to experimental results gained in 1972
[6]. The free gas volume changed in a way which is probably normal during a testing duration of eight to ten hours. The
results of these tests are the following that in case of existing cavitation the nondimensional pressure amplitudes of the blade
frequency are not affected by the free air content or by the chosen propeller revolutions. This result is confirmed by the extension of the cavitation photographed.
In contrast to this instance of existing cavitation the relative free gas vo1ume. has an extreme influence on the pressure
amplitudes K = of a propeller in a wake. In Fig. 17 some results of pressure amplitudes of the model propeller
of S.S. "Sydney Express" (HSVA-propeller 1917 - Zeise-design) are shown. Here the nondimensional pressure amplitudes K5
of the middle pickup (position 3) are shown for the advance coefficient
KT 0.61 and the cavitation number
C. =
PPv
=0.211 n27
-The abscissa is the measured relative free gas volumec. The
pa-rameter of the diagram is the chosen number of revolutions, i.e.
n = 15, 20 and 30 Hz, that means different pressure conditions in the test section according to the law of similarity of equal cavitation numbers. Mainly for the revolutions of n = 15 and n - 20 Hz, there are great influences on the pressure amplitudes by the relative free gas vo1umec,. Stereometric photographs of the blade in several positions
show that for a lower relafive free gas volume the cavity starts later than in case of the higher free gas volume. The
photographs underline the fact that the inception of the cavitation in the wake field and
conse-quently its disappearance,
influenced by the free gas volume, control the pressure amplitudes.
In Fig. 18 two sets of photographs for the observed propeller blaae in several positions are shown. The upper row is valid for the speed of revolution
n = 30 Hz, the lower for n = 15 Hz. The reason for the great difference in inception and extent
of the
ca-vitation is the fact that for the higher revolution the absolute pressure is lower (sometimes below zero) than for n 15 Hz; and
the absolute pressure is responsible for the expansion of the free gas bubbles. A more detailed explanation of this physical
behaviour shall be given in the last chapter of this paper.
Another interesting result of these investigations on the influence of the free gas content shall be mentioned
briefly, though the corresponding photographs cannot be shown here
because of
-29-more and -29-more stable, when the gas content was increased from lower to higher values, i.e. the intermittend
cavitation observed
here is a sheer model effect.
Before finishing this chapter, it has to be mentioned that the model speed of revolution o S.S. "Sydney Express"
regarding the Froude law of similarity was n = 9.7 Hz. According to Fig. 17 this influence of the free gas volume at this revolution
would be extra-ordinary. This speed could not be used because of the too low
tunnel pressure which is necessary for equal cavitation numbers of model and full scaie
It is obvious that the influence of the free gas volume is compensated to a certain extent by the greater revolutions, often used for cavitation tests.
The main results of the described measurements are as follows Increasing relative free gas volume for cavitation tests in a wake field ¿auses earlier inception and stronger extension of the cavity and therefore
increasing nondimensional pressure
ampi i tudes.
Cavitation tests for estimating the
propeller-excited pressure amplitudes should include the simultaneous determination of the relative free gas content and later on its possible control. The last statement
involves the question of the correct relative free gas volume in cavitation tests. The answer of this question is of highest importance for all cavitation
facilities, especially those with a free surface.
Moreover the main results confirm that the free gas volume scaling the cavity is of the same
importance as the correction of the wake field in the cavitation test.
In connection with the free gas volume it is to be mentioned here that a research project of the Special Research Pool at Hamburg in cooperation with the HSVA, The Technical University of Munich and D n V is going on. Besides cavitation observation
L-and pressure fluctuation measurements the free air content of the seawater shall be measured as the maintask in this project.
5. Theoretical Research on Cavitation Ince2tion with
A22lication of Bubble 0namics.
In Fig. 17 it could be observed that for the higher revolutions n = 30 Hz and additionally in all cases of the HSVA-propeller 1283
in homogeneous flow no dependence of the pressure amplitudes K
on the relative free gas volume ci. could be stated. On the other
hand for the lower revolutions (n = 15 Hz and n = 20 Hz) not only the pressure amplitudes on the plate but also the observed cavi-tation were dependent on the relative free gas volumec& to a high extent. Trying to find an explanation for this dependence one has to remind that, applying the value c, the behaviour of the single bubbles in a flow field with pressure gradient is neglected. Thus it was attempted to explain the differences in cavitation extent and pressure amplitudes for equal propeller loading and equal cavitation number, but different revolutions (e.g. Fig. 17) by means of a theoretical analysis of the dynamic expansion of single bubbles in a flow with pressure gradients. Such theoretical in-vestigations were carried out by Lederer (173 for steady hydrofoil flow in compressible water. The procedure was the following:
Iterative computations for the pressure distribution in compressible water with gas - content around hydrofoils were carried out accor-ding to the following formula
P
I
u2rrp
A-
31-(x-x)
dr1
-
ì4
(._ r1) . xs. Ayd
1rO -A r)OThe notation used can be found in sketch No. 3:
Skec'ì Wo3
The formula (5.1) is derived in a paper by Isay and Roestel 1183. in this connection gas means the content of free air in the water as well as the vapour in the interior of the cavitation bubbles.
The si ip velocity of these bubbles shall be, neglected and a further
assumption is that the bubbles are moving along streamlines. Using these assumptions the dynamic behaviour of a single bubble
+
(5.1)
in a temporally changing pressure field is described by a diffe-rential equation of the second order. This is thewell known Rayleigh-Plesset equation .. 4 1
*
2c5(5.2)
-
-4.RR
RIn this case R stands for the radius and R for the wall velocity of the bubble. The indes i is the designation for water r vapour, the index 2 for dissolved or undissolved air. The star belongs to the gas phase and Ö is the surface tension.
The growth of different initial radii
R0 was calculated by Lederer
(173 applying equation (5.2), which was solved with a Runge-Kutta method. The streamlines, along which the bubbles are moving, were
substituted by straight lines y
= n parallel to the x-axis.
For
further understanding of the procedure of Lederer [l7Jthefollowing ought to be mentioned:
During an air content measurement [153 Z = 1000 bubbles were measured, flowing through a cross-section F0 with a velocity u
in a time ç. Dividing
the measured radii (e.g. Fig 16) into
ranges
j
1,2 J, if the number of bubbles in a range is equal to Z0,then the gas volume of the flow is
'f
-
33-For the radii range R0 the number of bubbles is denoted by
o3
Ri
I\I
.4.\Vw
co
'J 3 (Rfl)3L
j4
So the number n3 of bubbles per unit volume of the flow is
z05=>
oj
O O O
(5.5).
(5.6).
Comparing an initial state ck at a point x = xo with a state at a
point x lying downstream and applying the conservation-equation, wnich means that the number of bubbles remains constant, one can
find
J
=
(M)
j'4
If the bubbles of the different bubble ranges contribute uni-formly to the compressibility, equation (5.7) leads to
(5.4),
(5.7)
(5.8).
which is referred to unit volume. Using the gas volume ratio
vg0
of the flow, then one 't.
For a point x (dównstream from the point x0) one can determine
3 3
--
3
The expansion of the radius of the single bubble from the
initial radius in the pressure field p(x) is calculated by means of the Rayleigh-Plesset equation (5.2). ¡f
s
(5.9)
R
=
B(R0,x)
(5.10)B
is the solution of equation (5.2), the local gas volume ratio in the hydrofoil flow can be derived from the equations (5.7) and (5.8) and it follows
3
3
(x,y)
3:4
(5.11).
As already mentioned, the precise determination of the streamline is neglected. Instead of this, the straight lines y = y parallel to the chord (x-axis) are regarded.
Knowing the pressure distribution p(x, y) along the lines y
=
according to equation (5.1) and using a nuclei distribution from a laser scattered light measurement (e.g. Fig. 16), the local gas volume ratio oc(x, y) of the flow can be calculated with the aid of equation (5.11).
The computations by Lederer L173 were carried out for two foil sections, a curved and an uncurved section. For the latter section
35
-results are shown in Fig. 19 to 21. The chordlengths for both were assumed to be ?A = lo cm.
The nuclei distributions of the computation were adapted to the results of the laser scattered light measurement[15J. Since more-over the growth of a single bubble depends on the absolute value of the initial radius R0, the measure bubble histograms were divided
into four ranges:
s
R01
5,m;
R02 = 35,m; R03 = 65,um; R04 . 95,,um.These ranges were applied in two different nuclei distributions for the calculations:
Nuclei distribution No. 1:
= 50;
o2 = 20; o3 = 5; o4 = i with
-= number of bubbles of the range j) Nuclei distribution No.2;
oi
= 200;02 = 20;
o3 i with c. = 1,3 . 10o
The increase of the number.çof the small bubbles by a factor four means practically no change in the free gas volume ratio of the
flow.
The occurrence of diffusion is neglected for this theoretical investigations, since this phenomenon develops too slowly, com-pared with the pressure changes on the foil section. Futherinore, the interaction between the different bubbles was ignored.
VG0
z 1,3 10
In order to show clearly the influence of the nuclei present in the flow, the expansion of a single bubble in the pressure field is displayed in Fig. 19. There the results of calculations for the r smallest bubble R01 and the greatest one R04 are shown. Fig. 19
J
is valid for the cavitation number
p
- p
=
EO.3
V
The pressure Po = 1 kp/cm2 and Po = 0.2 kp/cm2 in the flow
corres-pond nearly to the revolutions n = 30 Hz and n = 15 Hz in the ex-periments from 1974 [15J . The results of the computation, given
in Fig. 19 and plottet against the chordlength 2A, show clearly that the smallest bubble R01 is expanded after a short distance from the leading edge, if the inflow pressure is Po = 1 kp/cm2. The same bubble R01 is not expanded, if the inflow pressure is
Po 0.2 kp/Cm2. The reason for the latter fact is that the
pressure on the foil section does not reach stronger negative values because of the lower inflow velocity for the constant cavitation number 0.3. This can be found in Fig. 20, if the
pressure distributions for the two inflow pressures p0 = 1 kp/cm2
'\
and po = 0.2 kp/cm are compared in the region 0.01 0.06.Trie strongly negative pressurés therefore lead to the expansion of small bubbles. On the other hand a difficult problem of substant-ial importance appears, if the question should be answeredto what values the pressure in real water with free gas content may drop.
37
-Nevertheless Keller (see p. 96 in [163) found that during cavitation inception the absolut pressure on a body in the flow decreased
to negative values, whose magnitude depended on the nuclei distri-bution, i.e. the pretreatment of the water.
From Figs. 19 and 20 it becomes understandable, why the cavity
extent in Fig. 18 for n = 30 Hz is greater than for n = 15 Hz: The first reason is that the absolute pressure at the foil section for
n = 30 Hz reaches stronger negative values than for n = 15 Hz, and the second reason is that the number of small bubbles (see Fig. 16) is always greater than that of the great bubbles.
Additionally the great bubbles are further displaced from the foil section (screening effect).
The number of bubbles has in influence of the local free gas
volume c«x, (see eq. 5.11). In this connection the results calculated by Lederer r173 for the local free gas volume K(x,
on the suction side at a distance y/A = 0.005 are given in Fig. 21.,/' Here the nuclei distribution No. 2 for Po = 1 kp/cm2 attains the
greatest value c..(x, since the number of small bubbles R01
is four times as great as in the distribution No. 1. By the way, in this theorie with spherical symmetry for the bubble, the value c.= i means pure cavitation. This theory of the behaviour of single bubbles becomes meaningless, when the single bubbles grown and touch each other. In this relation of exspanding single bubbles
a question concerning Fig. 17 emerges. There the nondimensional pressure amplitude K5 on the flat plate is plotted against the relative free gas volume .But the que'stion is, whether the value c& is the right parameter for plotting the results, because,using
is ignored. But a better presentation of the results like Fig. 17 needs the measurement of smaller bubbles as measured in Fig. .16.
In this respect the recommendation given by the
ITTC-Cavitation-tö
Committee measure the bubble radii between 10,tm and 250,m should be supplemented: Nuclei should additionally be measured between 5 and 10pm radius.
At the end of this chapter on cavitation inception and bubble dynamics questions on future work should be discussed.
Normally the cavitation number and the thrust - or torque coefficient of model and prototype are kept equal for cavitation tests. This does not always lead to geometrically similar extent of cavitation (see Fig. 18), since the number and size of nuclei are important parameters in the reaction to the pressure field of the foil . Thus
geosim tests with hydrofoils or propellers should be performed with simultaneous measurement and possibly control of the free air content.
of the
Supplementary investigations'b'theory of bubble dynamics described
above should accompany the geosim tests. Furthermore for additional similarity conditions of cavitation tests it is necessary to know
the nuclei distribution in seawater around a ship. Other important factors are the basic behaviour of the cavitation facilities and the effect of installed flow regulators upon the free air content. These amount to a stronger consideration
of the quality of the flow medium for cavitation tests.
Efforts regarding these three tasks in cavitation research, namely geosim test for cavitating hydrofoils or propellers,
39
-tunnels and
determination of free air content in seawater
are being pursued in Hamburg at the Hamburg model tank (HSVA) and the Institute for shipbuilding (IfS) within the special research pooi for shipbuilding (SF8 98).
6. Conclusions.
The following conclusions can be drawn from the results presented
The hull surface forces excited on fast naval vessels by a cavitating tip vortex can be decreased by shifting the maximum circulation
to inner radii of the propeller. This method is probably useless for tankers and container ships, because of their wake distribution. In the theoretical field the estimation of the variation of the cavitating tip vortex in a ships's wake would be an interesting task. Afterwards it would be possible to account for the cavitating tip vortex in the total vibration excitation by the propeller.
Not only the technique for measuring the instationary pressure
distribution on propeller blades in a ship 's wake but also the three-dimensional lifting surface theory for the same purpose must be
improved. For the measuring technique the so-called direct method should be applied, i.e. pressure pick-ups mounted in the surface of the propeller blades.
The influence of the free air or gas content on cavitation
in-ception makes it necessary to determine the nuclei distribution during cavitation tests, where simultaneously
propeller-excited pressure amplitudes are to be measured. The
possible control of the free air content
would balueable
tool for these tests.
e
From the theoretical
investigations on bubble dynamics it can be
concluded that the theoretical model of the bubble and its behaviour in pressure fields' should be
checked by means of geósim tests. Another problem would be scale effects
on cavitation, which should be pursued with
7.
References
Lauaan, J.: Propellerkr.fte und
-vomente beim
geradlinigen Stoppmanöver.
(Propeller forces and moments during a
straight-lined crash stop). HSVA-Bericht
F )4/744 fUr den3FB 98.
f2
van Larnmeren, W.P.A., vari Manen, J.D.,
Osterveld, M.W.C.: The Wageningen B-Screw Series.
Transactions
SNAME Vol.
77
(1969)f3]
Laudan, J.: Einfluß der Kavitation auf die
Propel-lerkcräfte und -momente beim
geradlinigen
Stopp-manöver.
(The
influence
of the cavitation on the propeller
forces and torque during a straight-lined crash
stop). HSVA-Bericht Nr. F
8/76.
Laudan, J.: Einfluß der
Schrganströmung auf die
Propelierkräfte und -momente bei
verschiedenen
Fahrtsteigungswinkeln.
(Tne influence of the oblique flow on propeller
forces and torque for different advance angles.)
HSVA-Bericht Nr. F 9/76.
(Wake measurements with a series 60
model.)
Institut f1r Schiffbau,
Bericht Nr.
340
(1976).
[63
Weitendorf, E.-A.: Experimentelle
Untersuchungen
der durch kavitierende
Propeller erzeugteì
Druck-schwankungen.
(Experimental investigations on the pressure
fluctuations caused by cavitating
propellers.)
Schiff und Hafen,
Heft 11 (1973),
25. Bd.,
5. 1040-1060.
nj
Ackeret, J.: Ober stationäre Hohiwirbel.
(On stationary
hollow vortices.)
Ing.-Archiv (1930),
S.399-402.
f
87Weitendorf, E.-A.:
KavitationseinflUsse
auf die
vom Propeller induzierten
Druckschwankungen.
(Cavitation influences
ori the propeller
induced
fluctuations.)
Institut fUr Schiffbau der Universität
Hamburg,
bericht Nr. 338
(Sept. 1976).
Chijupiri, A.I.; Weitendorf,
E.-A.: Berechnungen
von
Druckamplituden mittels einer verbesserten
Quellen-Senken-Verteilung
fur
einen
kavitierenden
Spitzen-wirbel mit Knoten und Vergleich mit Messungen.
(Calculations of pressure amplitudes
by means of
an improved source-sink distribution for a
cavita-ting tip vortex with nodes,
and comparison with
measurements.)
Institut fUr Schiffbau der Universität Hamburg,
Bericht Nr. 339 (August
1976.)
10;
Xienappel, K.; Triebstein, H.
und Wagener, J.:
Messung der instationären Druckverteilung und der
Kräfte ari einem Propeller im
Schiffsnachstrorn.(Measurements of the instationary pressure
distri-bution and forces on a propeller in a ship'8 wake.)
Internal
DFVLR-AVA Report No. IB 253-76 C 04
(March 1976).
11
Kienappel, K.: Wiederholungsrnessung
der
instatio-nären
Druckverteilung eines Propellers im
Schiffs-nachstrom.
(Repeated measurement of the instationary pressure
distribution on a propeller in a ship's wake.)
DFVLR-AVA Report No. IB 253-76
J 09 (Sept.
Xrfte an Propellern
im Schiffsnachstrom.
(On the calculation
of the pressure distribution
and the forces on propellers in a ßhip'8 wake.)
Rep. No 309 Institut
für Schiffbau der
Universität
Hamburg (Oktober 1974).
r13
Isay, W.-H.: Moderne
Probleme der Propellertheorie.
(Modern problems
on propeller theory.)
Berlin - Heidelberg
- New York, Springer-Verlag
(1970).
van Oossanen, P., and
van der Kooy, J.: Vibratory
null forces induced by
cavitating propellers.
Trie Royal Institution of Naval Architects,
Spring
Meeting (1972).
)15
Keller, A.?., and Weitendorf,
E.-A.: Der Einfluß
'- J
dea ungelösten
Gasgehaltes auf die
Kavitations-erscheinungen an einem
Propeller und auf die
von
ihm erregten
Druckschwarikurigen.
(Influence of undissolved
air content on cavitation
phenomena at the propeller
blades and on induced
hull pressure amplitudes.)
Rep. No 321 A Institut für Schiffbau der
L161
Keller, A.?.: Experimentelle und theoretische
Untersuchungen zum Problem der modellmßigeri
Behandlung von
Strömungskavitation.
(Experimental and theoretical investigations on
the problem of cavitation in a flow with models.)
Versuchsanstalt für Wasserbau der T.U. München,
Bericht 26 (1973).
Lederer, L. :
Profilströmungen unter
Berücksichti-gung der Dynamik von Kavitationsblasen.
(Hydrofoil flow with regard to bubble dynamics.)
F(ep. No 31 Institut für Schiffbau der Universitat
Hamburg (Oktober 1976).
Isay, W.-H., and Roestel, Th.: Berechnungen der
Druckverteilung an Flügeiprofilen in gashaltiger
Wasserst römung.
(Calculations of pressure distributions
on
hydro-foils in water flow with
gas content.)
Zeitschrift für angewandte Mathematik und Mechanik
Fi g.
Caption
Noi
Test setup for pressure amplitudes
and
coordi-nates for measurements
2
Nondimensional blade frequency pressure
amplitu-des K3 in x-direction for
two propellers in
homogeneous flow
3
Cavitating propellers in homogeneous flow
Optimal propeller 1283 in homogeneous flow
under different cavitation
conditions
5
Different shapes of the
cross-section of
cavi-tating tip-vortices used
for calculations
6
Calculated pressure amplitudes
andwith
variations of the wavelength
X07
Calculated and measured pressure-amplitudes
(including those owing to a cavitating tip vortex)
on a flat plate
8
Measured instationary pressureon the
propeller-blades in a ship's wake
9
Measured instationary pressures on the
propeller-blades in a ship's wake
Fig.
No Capt i on
10
Measured inatationary pressures on the
propeller-blades in a ship's wake
11
Comparison between measured and calculated
pressures on propeller blades
12
Comparison between measured
and calculated
pressures distribution on propeller
blades
13
Comparison between calculated pressure and
cavity extent at radius
riRa
0.90
14
Nondimensional blade frequency pressure
amplitudes K5 in axial wake without
cavitation
15
Test setup for laser light scattering
method
16
Nucleus size histogram and fraction of relative
free gas volume
17
Noridimensiona]. blade frequency
pressure
amplitu-des Xp5 in an axial wake dependent on measured
relative free gas volume
18 1-LSVA propeller 1917 in
a wake for two propeller
revolutions with low free gas volume
19
Calculated (in 117] ) growth of
a single bubble
20
Calculated (in
fi7J )
pressure distribution
on a hydrofoil in stationary flow
21
Calculated (in
j17j )
local relative free gas
volume
on a hydrofoil in stationary flow
Sketch No.
1:Wave-like hollow vortex
Sketch No. 2:
Ellipsoidal hollow vortex
Sketch No.
3:
Notation for hydrofoil in
water with gas-content
B5
BL.
Direction of
flow
e= 30mm
ig.1: Test setup for pressure am plitudes
and coordinates for measurements
0.06
0.04 0.02 OfK3
..
in front of Prop.
-.05
Pos.Propeller 120; N'3
Advance- Ratio J = 0.8 03
Max. Circulation drawn to inner radii
0.12
0.08
0.04
¡n front of prop.
Prop.-plane
-0.25
2 3 O 'r Prop. pLane0.25
I.44
4J
0.5
a.x/R
5aIR' 0.109
a/Rs 0.109
g.2: Non dimensional
blade frequency
pressure amplitudes Kp3
Ifl
x-direction for two propellers in
homogeneous flow
-0.5
-0.25
25
0.5 Pos. i 4 5xIR
ATM
=3.00
2.00
1.75
1.50
1.25
1.1b
PropelLer 1283 ;
Ns 3
Advance - Ratio
J a 0.803
Fig.3: Cavitating
propelters in
homogeneous flow
P l283, Nz3
P 12h0
Nz3
Optimal distribution
Maximal circulation
of circulation
drown to inner radii
4 Optimut
propeLler
1283 in homogeneous
flow under
different cavitation
condition
Wavelength X0 = 600
ig. 5: Different shapes of the
cross
section of cavitating tip vortices
0 16
0.08
0.02
o0.40
0.32
0.24
0.08
0.16
-0.02
o- 0.5
oFig. 6: Calculated
pressure amplitudes
Kp3 und Kp6 with variation of
the wavelength Xo
60°
45°
150°
0.5 1.0 1.52.0 xIR0
I
.1
I
150°
i.
TAj,A;A
p
HSVA-Prop. 1283; homog .flow
Cavitating tip-vortex
Advance Ratio J = 0.803
m 24; RK0m /R0 :0.0252
Tip-clearance aIR0
0.109XA: 20°; X.t.p
00Cav.-num berGVA 1.14 .RK/RQ0.0143
0 24
90°
60°
<phri 0.2 0.1 O 0.2 0. 1 O 0.2 0.1 o 0.2 0.1 O 0.2 0.1 O
n
e
e
6VA *2.0
1.751.50
1.25
1.16Fig. 7:
Calculated and measured
pressure amphtudes (in
-cluding those owing to
a
ccivitating tip vortex) on a flat plate
3. 5. 9. 3. 6. 9.
in front of prop.
Pos.
Pl
P2
HSVA-Prop.1283;N3
Homogeneous flow
Advance Ratio
J 0.72 3. 6. 9. 3 .Prop. plana
P3
P4
Calculations with
VA 9.)(
3.6.harm Order
behind prop.
P5
RKam/Ra
Tip cearence a/R=O.1O9
2660
100410
0.010
1.75
700
15°31°
0.014
1.50750
15°43°
0.017
Measurement U
1.25 1.141020
110°
20°
20°
41°
46°
0.018
0.018
o Q. Q.
3
0.16-0.12
-0.16
nondirnens Rad. r/Ra 2 0.50
pressure side
suction side
0° 30° 90°
1800 2700 3300
o
o
A
9Fig.8: Measured instationary
pressures
on the propeller-blades in
a ship's
wake
ç
0 0.1 0.2 0.3 0.4 0.5
0.6
0.7 0.8 0.9-i
cp
0.12 O-0.0/.
- O. C 8-0.12
-0.16
-0.20
-0.2/.
-0.28
-0.32
-0.36
opressure side
suction side
AVA Propeller
non-dimens. Rad. nR0 a 0.90
0° 30° 90°
180°
2700 330°
D OA
90° 0.1 0.2 0.3 0./.0.5
0.6 0.7 0.8 0.9chordtength
Fig. 9: Measured instationary pressures
on the propeller blades in a ship's
Q? Q. Q. u