12 DEC. 1972
ìRCi IIEF.
D
NAVAL SHIP RESEARCH AND DEVELOPMENT CENTER
DOCUMENTATIE
D AT U ti:
-vo
DOCU N ENTA I E
Washlngton.D.C. 20007
TECHNIQUES FOR SHIP FRICTIONAL RESISTANCE
MEASUREMENTS
by
T.T. Huang and D. Lysy.
This document has been approved for
public release and sale; its distri-bution is unlimited.
DEPARTMENT OF HYDROMECHANICS
RESEARCH AND DEVELOPMENT REPORT
Lab,
v.
Scheepsbouwkunde
Technisché Ho
May 1970 Report 3307L
Onderafde.si
ische HogesCh00 iotheek van 1 cuwku"The Naval Ship Research and Development Center is a directed at achieving improved sea and air vehicles. It was David Taylor Model Basin at Carderock, Maryland and the Naval Ship R & D Laboratory) at Annapolis, Maryland. The Ship R & D Laboratory) Panama City, Floridà becamepart of
U.S. Navy center for laboratory effort formed in March 1967 by merging the Marine Engineering Laboratory (now Mine Defense Laboratory (flow Naval the Center in November 1967. Naval Ship Research and Development Center
Washington, D.C. 20007 SHIP CONCEPT RESEARCH OFFICE 0H10 DEPARTMENT OF ELECTRICAL ENGINEERING ASSO DEPARTMENT OF MAcHIMERY TECHNOI.00Y *700 DEPARTMENT OF MATERIALS TECHNOLOGY ASSO DEPARTMENT 0F APPLIED SCIENCE SYSTEMS DEVELOPMENT OFFICE 0H01 ERROL ANNAPOLIS CANOING OFFICER, TECHNICAL DIRECTOR
F
H
J-MAJOR NSRDC ORGANIZATIONAL COMPONENTS
DEVELOPMENT PROJECT OFFICES OIl 50. 80. 90 NSRDC CARD EROCK C0ANOER TECHNICAL DIRECTOR
I
DEPARTMENT OF HYDRONECHANI 500 DEPARTMENT OP AERODYNROIICS 600 DEPARTMENT OF STRUCTURAL MECHANICS 700 DEPARTMENT 0F APPLIED MAThEMATICS 000 DEPARTMENT OF ACOUSTICS AND VIBRATION000 NSRDL PANAMA CITY cDEBOANDING OFFICER TECHNICAL DIRECTOR DEPARTMENT 0F OCEAN TECHNOLOGY pilo DEPARTMENT OF MINE COUNTERMEASURES P730 DEPARTMENT OF INSHORE I WARFARE AND TORPEDO
DEFENSE I P740 DEPARTMENT OF AIRBORNE MINE COUNTERMEASURES P730 I * REPORT ORIGINATOR
DEPARTMENT OF THE NAVY
NAVAL SHIP RESEARCH AND DEVELOPMENT CENTER WASHINGTON, D. C. 20007
TECHNIQUES FOR SHIP FRICTIONAL RESISTANCE MEASUREMENTS
by
T.T. Huang and D. Lysy
This document has been approved for
public release and sale; its distri-bution is unlimited.
TABLE OF CONTENTS
Page
ABSTRACT i
ADMINISTRATIVE INFORÌ1ATION 1
INTRODUCTION i
METHODS FORMEASURINGSHÏPRESISTANCE COMPOÑENTS ...4
ANALYSTS OF PRESSUE AND SHEAR STRESS MEASUREMENTS
s
EXPERIMENTAL TECHNIQUES FOR MEASURING MAGNITUDE AND DIRECTION OF
Si-fEAR STRESS
HOT-FILM SHEAR PROBES ...9
DIRECTIONAL PRESTON PROBES
lo
RECOÌvffvNDATÏONS FOR SHEAR STRESS MEASUREMENT 14
CONCLUSION 15
ACKNOWLEDGMENTS 15
REFERENCES 26
LIST OF FIGURES
Page
Figure 1 - Coordinate System - 16
Figure 2 - Friction Plane Mounted to Towing Carriage and the
Locations of Hot.Fj1m.Shear Probe and Preston Tube 17
Figure 3 - Typical Hot-Film versus Preston Tube Calibration
Curves 17
Figure 4 - Typical Directional Response of Hot-Film Probe 18
Figure 5 - Detail and Mounting of Directional Preston PObe 19
Figure 6 - Plate - Details and Probe Locations 19
Figure 7 - DPP in Position on the Plate 20
Figure 8 - Turning Mechanism with all Plugs in Position, on
thePlate 20
Figure 9 - Details of Interference and Static Pressure Taps 20
Figure 10 - Response of Directional Preston Tube (Nose Angle
a = 45 Degrees) 21
Figure 11 - Directional Response of Center Tube (Nose Angle
c= 45 Degrees) 22
Figure 12 - DirectiOnal Response of th Two Side Tubes
(Nose Angle = 45 Degrees)
...23
Figure 13 - Directional Response of the Single Preston Tube 24
Figure 14 - Iñterference Effect 25
K o
Kp
KTM TL - TM = O). (e)TM
= TU (0) TM (e = O) TL (0) NOTAT I ONd Outer diameter of the Preston tube
ds Hull area element
ds' Project of ds on the midship section
ds" Project of ds on the half-girth plane Pressure force on the surface element
-p
Ff Frictional force on the surface element
i,j,k Unit vctors in x,y,z directions
TU - TM
111
(e
= O)9., m, n Direction 'cosines othe inward normal of the surface êlement
N Unit inward-normal vector of the surface element -;
P Pressure rotation
Dynamic pressure
P5 Statiò pressure
Difference between a Preston tube pressure reading p. and the
static pressure at the boundary
F Skin-friction resstànce
Rpv Pressure resistance.of viscous origin
R
Pressure resistancep
-Wave resistance Free-stream velocity Cartesian coordinates I APd log 4pv 2
t
y*10
4pv A Displacement weight.Nose angle of the directional Preston probe
O pirection between shear stress
t0
and the Preston tube orhot-film shear probe
e,1,
Trim angle
y Kinematic viscosity of the fluid
Orthogonal coordinates on the surface element
Unit vectors in directions
p Mass density of the fluid
t0
Shear stress at the ship hullAngle between the direction and the direction of shear stress
Subscripts .
DPP Directional Preston probe
SPT Single Preston tube
SL Lower static pressure tape
SU Upper static pressure tape
TL Lower. tube of the directional-Preston
probe--TM Center tube of the directional Preston probé
TU Upper tUbe
of
the directional Prèston probêABSTRAÇT
Totäl ship resistance consists of two components,
fric-tional resistance arid pressure (residual) resistance.
Fric-tional resistance can be obtained by the integration of the
measured shear stress distribution over the hull, and pressure
resistance can be obtained from the integration òf the
measured pressure distribution on the hull Pressure resistance
is further divided into a wave component and a viscous
com-ponent (form drag). Wave resistance can be measured by a
method which takes a longitudinal or a transverse cut of the
wave pattern. The expressions for computing the frictional
and the pressure resistançe from the measured shear stress
and normal pressure distributions are derived in this report.
Experimental techniques for measuing the magnitude as well as the direction of shear stress have been explored iñ
detail by hot-film shear probes. These probes are recommended for measuring the shear stress distribution on small models tested in towing tanks; hot-film shear probes with ambient temperature compensation and directional Preston probes are recommended for use.in tests of full-scale ships and
large-scale models.
ADMINISTRATIVE INFORMATION
This work was sponsored by the Naval Ship Systems Command (NAVSHIPS)
and funded under Subproject SF 35.421.006, Task 01713.
INTRODUCTION
Since the contribution of Froude nearl.y a century ago, total ship resistance has been assumed to be composed of two separate and. independent
parts: (1) frictional tesistance equal to te resistance of an equivalent plank or flat plate of the same wetted area and length as the ship and
(2) the remainder called ttresidual" resistance. I,t has been. a practical
engineering solution to extrapolate the resistance measured on a modelto that of a full-scale ship either (1) by assuming that the fricional
resist nce follows the Reynolds scaling law and that the residual resistance
follows t1e Froude scaling law .(Froude) or (2)b.y using a form factor to
distribute part of the.resiuài resistance Into viscous form drag (Hughes). These assumptions have never been satisfactory from a scientific
point of view. For instance, the. boundary layer on the ship is different from that on a flat p1ate, and the flow around..a ship hull is
three-dimensional in nature. Becäuse of the augmented fluid velocities around a
three-dimensional form, the skin friction of a ship hull is somewhat greater
than the corresponding friction of a flat plate. In addition, the gradual
energy loss resulting from viscous dissipation along tIe ship hull prevents
inviscid pressure rèstoration at the stern and produces form drag. If
eparâtiori occurs, there will be an additional form drag.. A combination of
skin friction drag an form drag is called viscous drag. When the body is
traveling on or near the suface, a wave system on the surface will be
created, and energy thát must be stipplied continuously by the ship to the wave system is called wave resistance. This résistance, in turn, manifests
itself in a pêsure distribution, over the hull, and the resulting net
fore-and aft-force is wave resistancé. It is known that the development of a boundary layer depends on the pressure distribution along the streamlines
around the hull. Since wave resistance is one of the parameters contributing to the total pressure distribution over a hull, it is apparent that wave resistance should play a role in the development of a boundary layer on the
hull,. The growth of a boundary layer, in turn, alters the flow lines near
the ship stern. This viscous effect will, in turn, modify the wave
resistance. At present the interdependence of the above-mentioned resist-ance components and the scale effects on these interactions are unsolved
problems.
Ländweber and Wu1 have reported that the viscous resistance measured by wake survey for various speeds was a sinuous line rather than the smooth
curvé that IS usually assumed. Townsin2 determined frictional resistance
indirectly by subtracting the total resistance from the measured pressure
resistance obtained by intgrating the measured pressure distribution over
the hull. Again he found that the frictional resistance oscillated with
speed. In addition, Shearer3 found interdependence of shear distribution
and Fröudènurnber. Although these recently measured interactioñs oi model
scale between the resistance components show that the basic Froude scaling
techni4ües need tO be reevaluated,-these findings do not imp'ove the
pre-diction of ship resistance from model testS since the scaling laws for
these interactions are not known. It has long been. recognized that a better
understanding of the real nature of the components of ship resistance and their interdependence may not only improve methods of prediction but may also lead to better procedures for minimizing full-scale resistance
The complicated nature of the flow arothid a ship hull has prevented
a successful treatment of thê ship resitance problem by ááömplêtely
analytical approach.. FOr inStánce, the accurate potntïaI flow field
around the ship at finite Froude number is not available. Conputatiôn of
three-dimensional ±urbulent boundary layers aloi hip fOrms has to rly on
the approxithated potential flow field as the computat.on schemi
fdrthü-lated by Webster and Huán'g.4 Th resUlts oLt
önutaioñs proide
only a qualithtive assessment fpr the real situátion, ànd thir procedure is not acceptabiê for predicting frictional resistance.
The increasing availability of modern instruméñtation and automatic
data processing has improved, experimental capability to such an extent that
direct measurements of individuai resistance cOmponents can now be ahieved.
It is important to select and to develop experimental techniquès which can
be applied to the measurements of resistance cOmponents of small ship
models (10 to 20 ft), large-scale models (80 to 100 ft), and prototype
shjps.,*
The results of such experimental series cOuld provide insight into
the physics of the individual resistance components which make up total
resistance and could determine the scaling laws of thêse interactions.
This report briefly discusses a number of experimental method for
measuring the resistance components of various scale ship models, describes
two techniques for measuring shear stress, presents experimental results
from these two techniques, and recommends further studies. The aim of the
present study is to advance experimental techniques for deriving ship
resistance components. These techniques will be applied t-o study resistance components of various scaled ship models at NSRDC.
*
METHODS FOR MEASURING SHIP RESISTANCE COMPONENTS
With the present. capability of instrumentation and automatic data
processing, it is possible to measur the nOrmal pressure and shear Stress
distributions over a ship huU through the use of a sufficient number of
flush-mounted pressure transducers and shear probes. The integration of a
shear stress distribution over a hull is the ship frjctiona]. resistance
consisting of the traditional flat plate frictiOn plus the additional skin friction due to augmented velocity resulting from flOw over thé
three-dimensional ship form. The integration of the fore-and-aft components öf the normal stress (pressure) over the hull surface is called the pressure
resistance and it contains the wave and form resistance çomnponents. The
wave resistance can be determined independently from the wave pattern by
such methods as the, "longitudinal or transverse" cüt.5 Form drag is then obtained by subtracting the measured wave resistance from the p±essure
resistance. Of course, the sumfi of thé integrated skin friction and the
integrated pressure resistance make up the total ship resistance which again
may be checked by he total 4rag measurements.
The. scheme shown belöw indicates the dervatiori of the components of ship resistance.
TOTAL SHIP. RESISTANCE (total resistance measUrement)
Frictional Resistance. (obtained by the inte-gration of shear stréss over the. hull surface)
Pressure Resistance 1.
(obtáined by the
inte-2
gration of normal.
(
stress (pressure))
Flat plate friction Form resistancê due to additional skin friction originated
from velocity
aug-mentation Form resistance Wave resistance measured by methods of lòngitudinal or transverse cut
The measurement of total resistance is a routine procedure for a
model, and it can also be achieved for a ship. A balance beam or modular
force gage is commonly used in the case of a model, whereas towing or jet
propulsion is required in the case of a ship. Pressure distribution on the
hull can be obtained by using a sufficient number of flush-mounted pressure
the longitudinal or transverse cut of the wave pattern behind the hull.5
However a reliable wave height sensor for measuring wave patterns is yet to
be developed, especially for use with large models and ships. Shear stress
distribution is relatively difficult to measure and involves a determination
of its magnitude and direction. Two promising devices available for this measurement are the hot-film shear probe and the directional Preston probe; both of these are discussed in detail inthe following sections.
ANALYSIS OF PRESSURE AND SHEAR STRESS MEASUREMENTS
Since skin friction and pressure resistance must be obtained from the integrations of measured shear stress ând pressure distributions over the ship hull, it is necessary to outline the computation procedure which
is simple but is necessaiy for planning data analysis.
For a stationary ship, a set of cartesian coordinates, x, y, and z fixed in the ship, is chosen such that the x-axis lies in the ship center-plane and parallel to the keel line, the x-y center-plane corresponds to the
undisturbed free surface, and the z-axis is positive upward. As the ship
moves in the positive x-direction at a given speed U0 on the calm surface,
it usually trims slightly down by the stern as shown in Figure 1. The
trim angle between the undisturbed water level and the direction of the
keel line is denoted by eT. On a hull area element ds (with unit inward
normal vector N whose directional cosinès are 1, m, n), there is stress
t0
acting tangentially to the surfaceand a pressure p normal to the surface. The pressure force acting on the surface elemént dis
F=pds(Zi+mj+nk)
where i, j, and k are unït vectors in the x, y-, and z-directions,
respectively. The òothponents of the pressure force in the x- and
z-directions are AF i p ds Z and tF . k = p ds r.
A set of orthogonal coordinates (, , n) with unit vectors (, ,
n) may be usêd to computethe drag from the shear stress vector r0 on the
ship hull. 1f the course of the ship is straight, the shear stress
dis-tribution is- synunetric with respect to the ship centerplane; then it i
necessary to consider only one side of the ship. We may let and be
tangential, to the surface element and be paia.11el to the y-z plane.
Furthermore, let n be parallel to the inward, normal of the surface element.
Thus, , , and n are -related tó i, j, k as
- a . b + b2 Va2 + b2 1/2 2 2 1/2 .2 2 -
112
2 2 Vc + d + e + d + e p/c + d + e c . d .. e3+
k and and1f
2.
+ m + = + mj +By orthogonality, i.e.,
n =
C C n = O, we have.2 .2
n
m +n
b, e=d, c=-
-- dm m 9.m
Then and are reduced to
n . m
-
3+
1/2
2 1/2 2The angle between and T0 may be denoted by 2; then the frictional fOrce
on the surface element can be written as
= ds [sin + cos.. 2
The components of the frictional force in the x- and z-directions are
''2 2
LF i=-t dscosc1Vn +m
f
and
The total resistancè can then be reréented. as
RT=
cos
dsJn
sin 0T dsccs
c os O dsJ
O IiÍ2
L 2 2 2 I T-'r isin Q:.
...
+cos
-- .-.-isin O
ds
(1)
v"
+m
nThe total dïspl-aceméntweight òf theship is equal to
$
''
0T ds+J
Pn COS 0T ds -Jr/
cos 2 sin+ i t i sin 2
T.
+ COS 1CO5 OJ
01/2
1/2
2 I T C I . m Zn I(2)
L
+ m - n + mIn these expressions, p is the total pressure on any element of
hull surface, but i,t is more convenient to measure only the change in pressure. Hence, p may be set equal to
d + where is the static
pressure on the element
at
restand
d is the measured change in pressure
on the element dring motion. Two çonditions of the integrated static
pressure on the hull at rest are:
and
J-p Z ds = sin
Jp
n ds
= cos 0TBy substituting
Pd + and the static condItions into Equations (1)
and (2),
one obtainsL1,
=-
JPd Z cos 0Tds+
J
Pd n sin 8T ds+JT
/ÇÇ2
cos 2 cos
0Tds
+It
. -._lin
O ds J °[2
2 1/2. 2 i T I/n + pin+m.J
7R-JPd
where R= R
+R-p. -w- -PV (10)f
J
d + Ç T [sien m ds = 0 (5)JO[
1,/2 21/2
2]n +m
n +m
Subtracting (5) from (4) produces
cos + sin 0T
T
+
J T
(cos
+ (sin 0T - 0T tan °T (sin
i. .12 2 245 cos 2 yn + in ds d cos 0T +
j
T coswhere 9ds is equal to the projêctiön of area element ds on the midship
section denoted by ds', i.e., y-z plane, and Vn2 + m2 . ds is the
pro-jectioI of the area element on the half-girth plane and denoted ds."
The skin-friction resistance and the pressure resistance may then
be defined respectively as:
rT. COS
I O R =1 ds" F jcoseT
r ds' cosThe measured pressure resistance R- Consists of wave resistance R and
- p...
w.
pressure fòrm drag Rp. Thus the total ship resistance Ft,. is made up by
the following measurable components:
8
12 2
Vn + m cos 2 sin O ds
o- T
+$in o,., -tan O,)1/.m2ds sin O
+5
dn cos ds
It is obvious that if the distribution p,
t,
and 2 ar measured..directy, the çQE1pation of Rf and R in Equations (7) and (8) can be
performed either by a high-speed computet or by a simple graphical
inte-gration. The wave resistance may he measured by th.e wave pattern behind
the ship ineperdçntly (i.e., by the method of longitudinal or transverse
5
cut). The pressu'e form rag is then obtained by Rpv = R
R.
Record-ing of the total resistance. is routine practice in towRecord-ing tank tests..Thus, an independent check of + RF is a]nipst always available.
EXPERI?vENTAL TECHNIQUES FOR MEASU.ING MAGNITUbE AND DIRECTION OF SHEAR STRESS
As shown in Equation (7), it is necessary to measure the
distri-bution of the magnitude of the shear stress and it angìé on the
half.-girths plane with respect to the x-4irectiQn (Figure lb) to obtain the
total skin friction resistance of the ship Two promising measuring
devices are considered in th.is repott.: the flus]i-mounted.hot-film shear
probe and the direçtiona1 Preston probç.
HOT-FILM SHEAR PROBES
The principle of hot-film shear probes is that. skin.friction. is a
function of electrical current required to mantaìn a platform film at a
constant temperature when placed ön the hull surface.6'7 .Linearization
öf the output from the hot-film anemometer with espect to shear stress
7 .
has been developed by L.ng. Nevertheless, the functioial relationship between the output of the anemometer and the shear stress is obtained through calibration, and slight nonlinear response is tolerable.
-, ...
-.
. . 6,7A flush-mounted,'hotfilm.shear probe (designed and built by Ling)
was used to dethonstrate the capability of measuring shear frèss in the.
NSRDC towing tafiks. .A strip of platinum film about 0.2mm wide and 0.8mm long was fuséd. uder-. high temératiire oñt'o th polishèd èfid of à pyrex rod 0.11 in. in diameter and 1 in. long. This hot-film shèar pÏobe was flüsh_T mounted on a 21-ft-long friction plane. A Preston tube was also attached
to'the plane adjacent to the hot.film sheatpobé (Figure 2). The
friction plane was towed at speeds frm 2 to 14 knots in the NSRDC.deep:
through the calibration curve of Patel.8 Figure 3 shows the outputs of the
hot-film anemometer versus the shear stresses. Note that the response of
the hot-film probe to the shear was linear.
The directional response of the hot-film shear probe was calibrated
by rotating the direction of thehot-fiim element with respect to the flow
direction. Typical results are shown in Figure 4. The directional
response is proportional to cosine O up to O = 50 deg.
Hot-film shear probes mounted flush with the hull surface do not
disturb the flow, and their response is independent of the pressure
gradient. However, the hot-film probes should be calibrated before and after test.
DIRECTIONAL PRESTON PROBES
The Preston method of measuring skin friction in the turbulent
boundary layer makes use of a circular Pitot tube resting on the wall.
The Preston tube pressure, together with the static pressure at the same
point, permits the computation of the skin friction at that point. The
use of the Preston tube is based on the assumption that there is a region
of dynamic similarity close to the wall where the flow is dependent only
on the local shear stress r, the mass density of the fluid p, its
kine-matic viscosity y, and a typical length parameter, i.e., the outer diameter
d of the Preston tube. The calibrations of a Preston tube reported by
Landweber and Siao,9 by Patel,8 and by many others are in good agreement.
The recent results of Patel8 will be used in the present work. The
cali-bration curves are:
10 x* = y* + 2 log10 (l.95y* + 4.10) (11) if 3.5 < y* < y* 5.3, = 0.8287 - 0.1381 x + 0.1437
x2
- 0.0060 x*3 (12) if 1.5 < y* < 3.5, and y* = 1/2 x* + 0.037 - (13) if y* < 1.5.Here x = log10 ( 2 T
d2
Lp.d\
*=
l('CT/0
I 4p\)2)1J
-bl0L
2 \ 4p \) TU -- f (e)K=
oTLN
), andp is the difference between the Preston tube pressure and the static
pressure.
Patel8 also found that a Preston tube can be used with acceptable accuracy (maximum error 3 percent) if the pressure gradient parameter is
limited to the range -0.005 < v/(pU) dp/dx < 0.01, where dp/dx is the
pressure gradient along the flow direction and UT =
(T0/p)'2
In order to obtain the direction of the shear stress, two three-tube
directional Preston probes were built and calibrated. Similar experiments
were done by Rajaratnam and Muralidhar,1° but their data were quite
scattered. In order to obtain a reliable calibration curve for the
directional response of the Preston probes, it is necessary to perform
certain experiments.
If the three-tube direction Preston probe is placed on the boundary
at an angle e with a directional shear stress
T,
a ratio of pressuredifferences among the three tubes, i.e.,
is a function of e only where the center tube is designated
two side tubes by TU and TL (Figure 5). The main objective
to determine the functional relationship between e and K0.
the pressure differences between pressure results from each
static pressure are functions of
t
and e, i.e.,i
P.d2
Td2
) KTM(e)TM'
=f1( °
2 e =[
4 2 j4pv2
4pv
Pud
Td2
) 2_f2(
218
pv
\4pv
= K(e)
11{,
PTh.d2]4pv
8=0 (14) by TM and the of the test is Furthermore, tube and the-(T0.d =
[
pmd21
(15) 2 y / 4p V 0=0 Cont'd If [p.d2/4 y2]00 and
SPT'4
v2]0 of the single Preston tube
(hereafter designated by SPT) have the same response with respect to T0 at
0=0 (as is found to be the case), calibration curves (11) through (13) can
be used here. If calibrations of KTM(0),
ru0'
and KTL(0) are provided,then the magnitude of shear
t0
can be obtained from Equation (15) with theaid of Equation (14) for determining
t0.
The aluminum plate shown in Figure 6 was mounted in the NSRDC 24-in.
water tunnel at a slight angle of attack (1/4 to 1/2 deg). Two directional
Preston probes (hereafter abbreviated DPP) shown in Figure 5 with nose
angles of 35 and 45 deg were calibrated against the shear stress angle B
at velocities of 10, 15, and 20 ft/sec. e is defined as positive for the DPP titled above the horizontal and negative for the DPP titled below the
horizontal. The DPP was pivoted in such a manner that readings at
different angles were taken at essentially the same location on the plate. A turning mechanism for the rotation of the DPP is shown in Figures 7 and
8. The number of turns of the threaded rod was calibrated against the
angle of the DPP to the flow so that the angles could be set from outside the water tunnel and all readings taken without having to reset the
velocity. During these experiments, the interference taps Il-14 and the static pressure taps Sl-S3 forward of the DPP were plugged (see Figures
5-9).
The upper, middle, and lower tubes of the DPP, as mounted on the
plate, were designated TU, TM, and TL, respectively. A four-channel
system of Pace differential pressure gages connected to digital voltage
meters (DVM's) was used to record data. The common side of the four
gages was connected t the lower static pressure tap SL, which was used as
the reference throughout the investigation. Lines from TU, TM, IL, and SU were connected to the other sides of the four gages and the pressure
differentials recorded.
A similar calibration of angular response was carried out for an
SPT. The interference taps shown in Figures 5 to 9 were used to determine
the effect of a similar probe located 6 to 24 in. forward of the DPP, with
the DPP aligned with the shear stress (O = O deg). Readings for the 35-deg
nose DPP were taken at all three velocities with the DPP dummy plug shown
in Figure 9 located at four upstream positions and for the SPT at the three
velocities with the SPT dunmiy at Location 14 only. The static pressure taps Sl-S3 were used to determine the approximate pressure gradient in the
immediate vicinity of the DPP. It was found that the velocity gradient
on the plate was negligibly small.
Calibrations of the turning mechanism for setting the angle O and the Pace gages were performed before and after the experiments in the
water tunnel and were identical. Because of difficulties with the turning
mechanism, each run was made with the DPP moving from the lowest (-50 deg)
to the highest (+50 deg) position. Four or five readings of the DVM were
taken for each data point. These were corrected for the instrument zero
drift (generally negligible) and record zero drift (generally < 0.1 in. of
water) before conversion to pressures. Because of the good linearity of
the calibration, this procedure introduced negligible error.
Readings for the SPT were taken simultaneously on two channels to
check the accuracy of the gage calibration and response. These were
treated as independent data points for purposes of analysis.
Examination of the data for SU indicated some interaction between
the DPP and SU and SL. It reached a maximum at the extreme angles when
the middle portion of the DPP was closest to SU or SL and caused the static
pressure to increase by a maximum of about 3 in. of water at 20 ft/sec. Consequently the reference static pressure was obtained at either SU or
SL, depending on the angular position of the DPP. For positive O (DPP
nearer to SU) it was assumed that the static pressure at SL was unaffected
by the DPP.
To nondimensiona].jze the data for the different velocities in the
most accurate manner, the
p reading at the zero angle to the shear stress
was used for reference pressure (not
SPT
Figures lO through 12 arethe nondimensional experimental results of the response of the directional
Preston probe with nose angle = 45 deg. Figure 13 is the directional
response of the single Preston tube. The present data from the SPT lie in
the middle of the data of Rajaratnam and Muralidhar1° and are slightly
different from those of Sigalla.11 Readings of the center tube of the DPP
with o. = 45 deg and the SPT were identical for a given T0 with O = O deg. Thus the single Preston tube calibration curves can be used for the DDP
with o. = 45 deg. However the reading of the center tube of the DPP with
o. = 35 deg was slightly less than that of SPT. No further application of
the DPP with o. = 35 deg is recommended.
The interference effects of a similar probe located at various
locations upstream of the DPP are shown in Figure 14. An upstream probe
tends to increase the shear stress downstream. On the basis of the results in Figure 14, it is suggested that if a large distribution of Preston probes is needed to determine the shear stress distribution on a ship hull, downstream probes should be placed at least 4 ft away from
up-stream probes to avoid interference effects.
RECOMMENDATIONS FOR SHEAR STRESS MEASUREMENT
Hot-film shear probes mounted flush with the hull surface are recommended for the measurement of shear distribution on the smooth ship
hull because (1) they do not disturb the flow, (2) their response is
inde-pendent of the pressure gradient, and (3) their directional response is
found to be approximately a cosine function of the angle. The hot-film technique can presently be used for measuring shear stress distribution on ship models in towing tanks where the temperature variation is expected to
be small. However, for tests where varying ambient water temperature is a significant parameter, suitable techniques for the ambient temperature
compensation of hot-film shear probes are yet to be developed. A dummy probe connected to the opposite arm of the bridge to the measuring probe
should provide the feature of temperature compensation. Further
investi-gation into this technique will be undertaken.
At present the directional Preston probe and/or the single Preston
tube are the alternatives for measuring the shear stress on large and
full-scale ships since they are relatively insensitive to tempexature
ambient variation.
Before actual measurements öf skin frictiö resistahce of a ship can be performed, techniques must be deve.pped for handling a large number
of probes and for processing 1-arge amounts of datä by modern data-processing methöds.
CONCLUSION
It is recommended that measured totaiship resistance be determined
through jts measurable components. Frictional resistance can be obtained
from the integration f shear stress over a
hull,
and pressureresistáncecan be obtained fröm the integration of the nôrmal press acting on a
hull. Wave resistance may be directly measured by the longitudinal or
transverse cut of the wave pattern. The results of the recommended studies would provide insight into the physics of the itidividual resistance com-ponents, their interactions, atid the scale effect of their interactions;
they might also lead to procedures for minimizing full-scale resistance. Experimental techniques for measüring the magnitude and direction
of a shear stress distribution havé. been exlorèd in detail. Hot-film shear probes are recommended for use in towing tank tests of small models
but at present hot-film probes. with ambient.temeratùre ¿ompensation or
directional Preston probes should be used for tests where varying ambient
water temperatureis a significant parameter. .
ACKNOWLEDGMENTS
This wörk was done ufìde± the úérvi-ion of Mr.: G.G. Cóx;
his
encouragement and advice are gtatefully acknowledged. The hot-film shear
probe and the anemometer were supplied by Professor S C Ling of the
Catholic University of America.
Figure la - Pressuré and Shear Stress Acting
oi the Ship Hull
ACTUAL
WL-lO 9 8 7 6 5 4
AP
Figure lb Shear Stress Acting. Qn:'the.Half-Grth Plane
Figure 1 Coordinate System
16
LWL
D
2I-0 20- O SIDE PLATES-ALUMINUM 20' 4x 1!4' 5.0 4.0 LO
TOWING CARRIAGE DYNAMOMETER
14-5'
HOT-FILM SHEAR PROBE-.4
PRESTON TUBE
Figure 2 - Friction Plane Mounted to Towing Carriage and the Locations of Hot-Film Shear Probe and Preston Tube
17 V2" .
o
. O 0.001 0.002 0003 0.004 0.005 0.006 0.007r(PSI), BY PRESTON TUBE
1.4 1.2 LO 0.8 0.6 0.4 0.2 o CURVE OF OS O
o
o
18 O IN DEGREESFig.ire 4 - Typiçal Directional Response of Hot-Film Probe
21"
7MA MiA
WASHERSi
FLOW
FLOW
NUT
Figure 5 Détail and Mounting of Directional Preston Probe
X
X
XX:
SANDPAPER STRiP (LOST DURING TESTING)
1/4" RADIUS LEANG EDGE+ SIDES
O.072"O.D., O.040"I.D. STAINLESS STEEL TUBING 3 TUBES SOLDERED TOGETHER
78'
6" OPP SOLDERED TO 8-32x 11/2 BOLT
14 13 12
Q-- ,
oXX MOUNTING POINTS
Il-14 INTERFERENCETAPS,6"APARTAND6"FORWARDOFDpp
Si-53 STATIC PRESSURE TAPS, 1'APART AND 1" FORWARD OF DP.P
SU.SL STATIC PRESSURE TAPS, 1" ABOVE AND BELOW DSP
11F HTFILMPROBE
OPP DIRECTIONALPRESTONPROBE
STATIC PRESSURE TAPS ARE V16" DIAMETER
Figure 6 - Plate - Details and Probe Locations
1 9 a NOSE ANGLE PLAT E TURNING BAR Xx TU XX
H_'i"
- 1/2" ALUMIÑUM PLATE'
&.
(
t'
Figure 7 - DPP in Position on the Plate
INTERFERENCE TAPS
Figure 8 - Turning Mechanism with all Plugs
in Position on the Plate STATIC PRESSURE TAPS
Figure 9 - Details of Interference and Static Pressure Taps
PLUG
DPP DUMMY
1.2 0.8 0.4 O 0.4 0.8 1.2 TL TM K0 n n rTu rTM 450
_-TU DPP : U0 ( F P S)Qio
015.
TU TL- TM
- TM
1.6 -50 -40 -30 -20 -10 0 10 O IN DEGREESFigure 10 - Response of Directional Preston Tube (Nose Angle a = 45 Degrees)
20
50
30
40
KTM Ap(0 0)
111
ii
07450
U0(FPS)0
15020
DPP -50 -40 -30 -20 -10 0 10 20 30 40 50 60 O IN DEGREESFigure 11 - Directional Response of Center Tube (Nose Angle a = 45 Degrees)
1.1 1.0 0.8 0.6
I-0.4 0.2 O
1.2 O. 8 0.4. - 0.4 - O. 8 - 1.2
-50
-40-30
-20
-10
0 10 20 30 40 50 60 O IN DEGREESFigure 12 - Directional Response of the Two Side Tubés (Nose Angle
1.2 1.0 0.8 0.6 02 -0.2 -50 -40 -20
-lo
O 10 O IN DEGREES 30Figure 13 - Directional Response of the Single Preston
Tube 40 50 60 L KsP=1\PSp,.(00) SPT()
(
1L
He
\)
'
\
\ RAJARATNAM
MURALIDHAR DATA REGIONOF AND, 10SIGALLA1\%\
U0 c4> IQ
o
020
UQ(FPS) 10 15 : I H L 1 T0 -I I I1.20 1.15 'o 110 1.05 1.O iill K K. NO PLUG 1OFPS 20 FPS
.
Qio FPS (KTU + NO PLUGI
4. o 6" 12" 18" 24"DISTANCE OF DUMMY DPP UPSTREAM OF THE DPP
2
3
4
PLUG LOCATION
REFERENCES
Landweber, L and Wu, J., "Formal Contribution on Resistance,"
Tenth International Towing Tank Conference, London (1963)
Townsin, R.L., "The Frictional and Pressure kesistance of Two
'Lucy Ashton' eosims," Quart. Trans. Roy. Inst. Nay. Arch., Vol. 109, No. 3 (Jul 1967).
Shearêr,:J.R., "The -Experimental -Determination-of the Components of ship Resistance for a Mathematical Model," Quart. Trans. Roy. Inst.
Nay. Arch., Vol. 107, No. 4 (Oct 1965).
Wbster, W.C. an Huang, T.T.,"Study of the Boundary Layer on
Ship Forms," Hydronautfcs, Inc. TechPical Repon 608-1 (Jan 1968).
Eggers, K.W.H. et al., "An Assessment of Söme Experimental
Methods for Determining the Wavemaking Characteristics of a Ship Form,"
trans. Soc. Nay. Arch. and Mar. Eng., SNA!t, Voi. 75 (.1967).
Ling, S.C., "Heat transfer Characteristics of Hot-Film Sensing
Elements Used iti Flow Measurethent," Trans. Am. Soc. Mech.. Eng., ASME, J. Basic Eng, Vol. 82, Nô. 629 (1960).
Ling, S.0 et al.., "Application of Heated-Film Velocity afld
Shear Probes to Hemodynamic StudIes," Circulation Res., Vol. XXlll No. 789
(Dèc 1968).
Fatel, V.C., "Calibration of the Preston Tube and Limitation on
Its Use. in Pressure Gradients," J. Fluid Mech., Vol. 23, (1965), pp. 185.-208.
Landweber, L. and Siao, T.T., "Comparison of two Analyses of
Boundary-Layer Data ona Flat Plate," J. Ship Res. (Mar 1958).
lo. Rajaratnam, N. and Muralidhar, D., "Yaw Probe Used as Preston
Tube," Aeron J. Roy. Aeron. Soc., Vcl. 72, No. 1060 (Dec
1968).
li. Sigalla, A., 'Experiments with Pitöt tubes Used for Skin
Friction Measurement," British Iron afld Steel Research Msociation Report (Mar 1958).
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UNCLASSIFIED Seèurit
C1iiifiiiiói
FORM 1473
(PAGE I) I NOV 651 S/N Ò1Ô1.807.6801 UNCLASSIFIED Security ClassificationDOCUMENT CÖNTRL DATA -. R & D
(Scç_urity c!assifiration oftitle, bodyof absr,oct and indcsing annotation must be entered s'ben the overa!! report is cJaSsi(led)
(ORIGINA TINGACTIVITV
Naval Ship Research and Development Center Washington, D.C. 20007
Za. REPORT SECURITY CLASSIFICATION
Unclassified.
2b. GROUP
3.REPORT TITLE .
-TECHNIQUES FOR SHIP RICTIONAL RESISTANCE MEASUP.EMENTS
4. DESCRIPTIVE NOTES(Type ofrepon and inclusive da(es) -
-5. AU THOR(S) (FiI'.st name middle ini(ial,last name) ...-
-Thomas T. Huang and Dusan Lysy
6. REPORT DATE
May 1970
76. TOTAL NO. OF PAGES
33
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b.PROJECTNO.
SF 33.421.006 Task 01713
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s:
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Il. SUPPLEMENTARY NOTES (2. SPONSORING MILITARV ACTIVITY
NAVSHIPS
13. ABSTRACT .
Total ship resistance consists of two components, frictional resistance and pressure (residual) resistance. Frictional resistance can be obtained by the integration of the measured shear stress distribution over the hull, and pressure resistance casi be obtained from the integration of the measured pressure distribution on the hull. Pressure resistance is further dIvided into a wave component and a viscous component (form drag). Wave resistance
can be measured by a method which takes a longitudinal or a transverse cut-of the wave pattern. The expressions for computing the frictional and the pressure resistance from the measured shear stress and normal pressure dis-tributions are derived in this report.
Experimental techniques for measuring the magnitude as well as the direction of shear stress have been explored in detail by hot-film shear
probes. These probes are recommended for measuring the shear stress
dis-tribution on small models for measuring the shear stress disdis-tribution on
small models tested in towing tanks; hot-film shear probes with ambient temperature compensation and directional Preston probes are recommended for use in tests of full-scale ships and large-scale models.
hi
Unclassified,
DD
1 NOV 45 IFORM 1473 (BACK)(PAGE 2)
Securtty Classification
UNCLASSIFIED
Seéuritj Classification
14. - -
-KEY WORDS - LIN,( A- -- LiNK Ô LINK C
ROLE WT ROLE WT FOLE Wr
-Ship Resistance Components Shear Stress Measurement
Magnitude and Direction
Hot-Film Shear Probes Directional Preston Probes