U
National Maritime Institute
Manoeuvring Experiments using
Two Geosims of the <Esso Osaka
by
I W Dand and D B Hood
NMI R163
May 1983
National Maritime institute
Feitham
Middlesex TW14 OLQ
Te1:0-977 0933 Telex:263118
MsIIwsg 2, 2628 CD Dellt
LO$5àiwi.F O15.7816
This report is NNI Ltd Copyright but may be freely reproduced for all purposes other than advertising providing the source is acknowledged.
MANOEUVRING EXPERIMENTS USING TWO GEOSIMS OF THE 'ESSO OSAKA'
BY
I W DAND and D B HOOD
Summary
Two geometrically-similar models (geosims) of the VLCC 'Esso Osaka' have been used in a series of constrained and free-running manoeuvring experiments in various water depths. Forces, moments and trajectories have been measured in order to derive the coefficients needed for the NMI Cruising Speed
Manoeuvring Simulation model. Detailed results are presented and discussed and some limited simulations are compared with both free-model performance and that of the ship. Some conclusions are drawn regarding scale effect on manoeuvring predictions derived from model measurements.
CONTENTS Page Introduction 1 Experimental Details 1 2.1 Ship Models 1 2.2 The Experiments 3 2.3 Analysis 5
Results Obtained and Discussion
3.1 Constrained Model Experiments 6
3.1.1 Resistance Experiments 6
3.1.2 Bollard Pull Experiments 8
3.1.3 Oblique Tow Experiments 8
3.1.4 Rudder Angle Experiments 9
3.1.5 Combined Drift and Rudder Angle Experiments 9
3.1.6 Rotating Arm Experiments 10
3.2 Free Running Experiments 11
Manoeuvring Coefficients and Simulation 13
4.1 General 13
4.2 Simulation Model and Manoeuvring Coefficients 14
4.2.1 Linear Motion Coefficients 16
4.2.2 Rotary Motion Coefficients 19
4.2.3 Remaining Coefficients 19 4.3 Simulation Results 20 General Discussion 22 Conclusions 24 References 25 Acknowledgements 26 Nomenclature 27
Introduction
In July and August 1977 a comprehensive series of manoeuvring trials was carried out on the 278,000dwt tanker 'Esso Osaka' in the Gulf of Mexico (ref. 1). A
variety of manoeuvres was carried out in three water depths - deep, (water depth (h)/at-rest draught (T) = 4.2), medium (h/T = 1.5) and shallow (h/T = 1.2). For all trials the ship was loaded to a draught very close to the Summer Freeboard waterline and measurements were made of ship track, engine r.p.m., forward speed,
rudder angle, lateral speed, rate of turn and change of heading.
The compendium of results thus produced, while of interest in their own right, also provided a valuable source of data with which to compare predictions based on measurements made with geometrically-similar models (geosims). Accordingly the Maritime Administration of the United States Department of Transport initiated the Joint International Manoeuvring Programme (JIMP) to encourage ship model
basins throughout the world to test models of the 'Esso Osaka' on a co-operative basis using the full-scale data for comparative purposes. The National Maritime
Institute, with funding from the Maritime Technology Committee of the UK
Department of Industry took part in JIMP; this report describes the work done and presents some of the results.
Prior to NMI's involvement, model experiments had been carried out at Hydronautics
Inc. (ref. 2) and the Davidson Laboratory of the Stevens Institute in Hoboken, New Jersey. The models used at both these establishments were made available and it was decided that NMI would provide a third geosim. This allowed the Stevens and NMI models to be tested in a complete programme of experiments normally carried out by NMI to obtain manoeuvring coefficients. It therefore provided a unique opportunity to study the effect of model scale on measured manoeuvring data.
Experimental Details
2.1 Ship Models
-2
to be too large for all except the largest of NMI's towing tanks. As this would have restricted experiments to oblique tow and planar motion mechanism tests in deep water only, it was decided in the first instance to concentrate attention on the other two models. However a comparison of all three models and the ship is made in Table 1:
TABLE 1
Item Ship Models
Hydronautics Stevens NMI
Length between perps. L(m) 325.0 7.257 1.625 3.536
Breadth mid, B(m) 53.0 1.183 0.265 0.577
Trial draught, T(m) 21.8 0.487 0.109 0.237
Trim,
t
level level level levelDisplacement, volume V (in3) 311,669 3.470 0.0389 0.401
Block Coefficient, CB 0.830 0.830 0.830 0.830
Midship Section Coeff., C, 0.998 0.998 0.998 0.998
Prismatic Coefficient C 0.830 0.830 0.830 0.830
Scale 1:1 1:44.783 1:200 1:91.91
Rudder area! (L.T) 0.0169 0.0169 0.0169 0.0169
Number of rudders 1 1 1 1
Rudder Type balanced balanced balanced balanced
simplex simplex simplex simplex
Number of Propellers 1 RH 1 RH 1 RH 1 RH
Diameter, D (m) 9.10 0.204 0.044 0.099
Blade Area Ratio, B.A.R. 0.682 0.682 - 0.683
Mean Face Pitch, Pm(m) 6.507 0.146 - 0.077
Number of Blades 5 5 4 6
and along the line of the bilge.
A six-bladed stock NMI model screw propeller was fitted whose parameters were similar to those of the full-scale propeller. This was driven by a 75 watt DC printed-armature motor.
The Stevens model was fitted with similar printed-armature motor and both models had rudders which could be set to any required rudder angle, S, in the range
.35° tS 350
For the free-running experiments the NMI model was fitted with proportional radio control of rudder and shaft revolutions. It was also equipped with a heading gyro and a transmitter for the NMI ultra-sonic position-plotting equipment.
Heading signals, drift angle, rudder angle and shaft rpm were telemetered ashore where they were combined with the position-plotting signals to give information on
position, speed, heading, drift angle, rate of turn etc. during the experiments.
2.2 The Experiments
A set of constrained model experiments was carried out on the Stevens and NMI models. Although the results were obtained over a range of drift angles from 00 to 1800, we concentrate in this report on experiments and analysis relevant to the NMI 'cruising speed' simulation model. This is valid for drift angles up to about ± 200 and relates to the case where the ahead or astern velocity
of the ship dominates the motion. This is comprehensively documented in reference 3 and has formed the basic mathematical model used in several UK ship simulators. As it is therefore widely known it seemed appropriate to compare its predictions with ship behaviour and also to use it as a comparison with other, similar, models world-wide. Results from the large drift angle experiments will be reported at a later date.
Accordingly the experiments and parameter ranges considered in this report are given in Table 2. No planar motion experiments were conducted.
4
Experiments 1 to 5 áove were carried oüt.in the
no.2 towing, tank with a deep
water section ll9m long, 6 lm wide and 2 74m deep and a shallow water section
BOrn long whose depth can be varied from zero to
0.. 5Gm., The rotating arm,
experiments were carried. out in. the 30m square
4A tank with a maximum epth
of 2.44m.
. Figure 3 shows the Steven
model under test. on the rotating arm.
ForOes and, moments on the NMI model were
measured using a four-component
strain-gauged dynamometér mounted in.
tie mol and measuring in body axes.
This
instrument
was too large for the Stevens. rode1 so
fot this, surge and sway
forces, together with yaw moment, were initially, measured using threemodu ar
force gauges of 50N capacity.
They wer.e mounted on an earthing beam aboye the
model, the forces being transmitted to them via pins fixed to the force gauges
and lightweight rollers motinted
n the mo1el.
This arrngement was satisfactory
EXPERIMENT
h/1
r*
pRIFr ANGLES
RUDDER ANGLESS.
1. Resistance and
1.2
0.02-0.12
0.0
00.
Propulsion
1.5
0.02-0.13
0.0
0 00.02-0.16
0.0
0 02. Oblique tow
1.2
0.034
0.0
-25° to +25°
01.5
0.051
0.0
-16° tO +16°
00.102
0.0
-25° to +25°
.03. Rudder angle
1.2
0.34
0.0
0-30° to +300
1.5
0.068*,0.085**
0.0
0.0
0.102
.0.0
0.0
4. Bollard Pull
1.2*
0.0
0.0
0.0
..15*.
0.0
0.0
0.0
'I0.0
0,.0
0.0-5. Comb'ned Drift Angle
1.2
0.34
0.0
0° to -20°
-30° to +30°
and Rudder Angle
1.5
.0.068*,0.085**
0.0
0° to -20°
-
0.102
.0.0
00 to -20°
6: Rotating Arm
1.2*
0.051
0.29-0,79.
-25° to 20°
01.5*
0.051
0.29-0.7.9
!' 0 - -0.068*,,0.l02**
0.14**_9.79*
U 07. Free Running
. .1.2*
-
-
-30° to +30°
1.5*
. . .0.102
. .--
.--.---
. --. .-N.B. *
= NMI model only
TABLE 2
for sway for.ce and, yaw mome±t, theasurement,:but unsatisfactory. for, the measurement
of surge force.
The surge force gauge was therefore :relaced by a sensitive
arallel-liiik straIn-gauged fiexure.
Freerunning eperiments were run in- the 60m square butdóor thàhoeUvring
ta±-k.using the NMI model dnlr:.
As mentioned in section 2.-i above,' the model was fully
instrumented, the comp]ete model- and shore-based System being shown
in
Figure 4.
In the constrained mQdel experiments, results were integrated Over a period of 30
seconds to give mean values.. Preliminaiy anal'sis. were. óaried out using a, Commodore
?ET:micro.computerduting the experiments and all non-dimensiona1sèd raw data
storedon floppy di. On-line analysis. of the free-model résults
was
ôàrried out on a Tektronix 4051: systeIn, results being stored
on punched. paper
tape for later more detailed analysis.
2.3
Analysis
The resuith obtained in. the experiments have generally been non-dimensionaliSed
ccording to the following, well-known, scheme using the axis system
á.ndefin-itions of Figure 5.
x' =X/½pLU,.
Yl = Y/½LU0.
,N". = N/½PLU
here X, Y, N are surge and sway forces together with yaw moment
Do
is a reference velocity and
p
is water density
As stated above, initial data processing was carried out using a micrO.cOmputer
during the exper-iments.
miS' entailed: conversion of: the amplifier outputs. to
forces and moments using 'appropriate' calibration factos (obtained before -the
experiments) ,
OorréctIng for zero values, nohdimensi'onal.isation: and plotting.
The purpose of 'this report, and indeed one of
ththain aims of the project, is
to present this raw data in its entirety and, incidentally, to compare results
cbta-ined with two gebsiins.
However, only kinematic results are available from
the full-scale. tra1s of ref. 1 so tat in order to use these for comparative
purposes,, it was necessary to relate the constrained model measurements o the 'free running' trial measurementS.
This was done, naturally, by means of a simulation thode-1 and as mentioned
above, the NMI tcruislng speed' model was used This entailed further off-line analysis of the. data to obtain the coefficients using methods described in
reference 3.
-Results from the rotatinq arm were analysed to remove inertial and translatory effects leaving 'rotary' surge and- sway force and yaw moment coefficients
XR', 'ER' and NR'. ThiS was done both by the method of referenc 3 in hich.
part of the simulation model is used as an interpolator,' and also by a, straight
subtraction of the measured xanslãtory effects at the appropriate. condition.
These calcuIat-Ons were also carried out on the micro-coputer.
3. Results Obtained and DiscussiOn
Results Obtained from the experiments are presented here in graphical form; the numerical data from which the various figures were obtained is held at NMI
Ltd.
The results are segregated for ease of preSentation; each main series of experiment data is discussed in turn and, where appropriate,, cOmpariSons between results obtained with the .NMI and Stevens geosiths are made.
3.1 constrained Model Experimens
3.1.1 Resistance Experiments
Resistance measuréehts obtained at each depth/draught ratio are shown for
both models in Figure 6. As might be- èxpected.some differences between results from. the twO geosims are apparent. The Reynolds Numbers of the experiipes
point.
TABLE 3
It is seen from Table 3 that resistance values for the Stevens model were obtained at a limited number of speeds only. It may be noted from Figure 6 that, not unexpectedly, resistance is not proportional to the square of the speed over most of the
range. As will be: seen later, coefficients in the simulatron model for hull resistance were obtained locally at the reference speed, at which a
was assumed to apply.
Resistance values for all conditions were estimated using references 4 and 5 and results are shown on Figure 6 from which it is seen that in deep water reasonable agreenènt was obtained wjth the i4I model measurements. The limited measutements made with the SteVens model and their scatter makes comparison of estimation and measurement difficult, but -itappeãrs that the estimated values do not disagree significantly with the measurements. Shallow water estimates fOr theI model
using reference 5 consistently under-estimate the measured values.
Propulsion experiments were also rn to find the model self-propulsion point fOr
each model at each depth. It should be noted that the coefficients or the NMI cruising speed equations are obtained at model- rather than ship self-propulsion point Both constrained and free running experiments are run at this condition so that all experiment results are consistent The propeller model incorporated in the NMI equations (ref. 6) uses data at model self-propulsion point so that at full-scale the correct propeller r p m /speed relationship is obtained The
above should be borne in mifld if the data presented here is to be used with
another propeller simulation model, should this operate at the ship self-propulsion
h/T NMI Model Stevens Model
3.65.lO to 2.92.106 4.84.lO, 5.8l.lO 1 5 3 65 lO to 2 47 106 2 90 i05, 4 84 lOs, 5 81 l0
3.1.2 BollardPull Experiments
Bollard pull experiments ze±é cärriéd out at all depths tO Obtain:
- screw bias data fOr the sway and yaw equatjon
- bollard pull data as part: of the propeller thrust Odel.
Results are shown in Figure 7 from which 'it is seen that an expected variation of X' with (n')2 was obtained. It 'is also notable that the effect of' shallow water is to increase X" 'at a given n'.
The variation of Y' with n' shows some scatter fOr n' < 0 and there appears to be a tendency for Y' to change sign as h/T decreases for astern revolutions.
Generally good agreemnt is found with N' at all depths for n' < 0 but for n' > 0 some scatter is apparent with disagreement between the NMI and Stevens
model results in deep water. It may be noted however that the turning moment due to screw bias for n' > 0 generally increases with decreasing underkeel clearance.
Bollard pull results for the Stevens model were obtained in deep water only; they ar shown in figure 7.
It should be noted that the reference shaft revolutions n0 used in the bollard p11 analysis' were those appropriate to the reference velocity U used to compute
the non-dimensional force and moment coefficients.
3.1.3 Oblique Tow Experiments
The oblique tow experiments were carried out with rudder, amidships 'at a' speed
representative of' a manoeuvring speed in the depth of water under coñsideràtion. The results are shown in Figures 8th' 16 in which results from both models 'are compared. I is apparent that fOr the sway force and yaw moment there is good
agreement between the results obtained from, both models over a drift angle
range of about _8o to +80. At angles, larger than thrs where non-linear viscous-dominated effects become important the results of the two models diverge slightly although there is still a large measure of agreement.
3.1..4 Rudder Angle Experiments
Results obtained from runs at zero drift angle, model self-propulsion and .
-contant speed, in which rudder. angle was varied, are shown in Figures 17 to
25, These indicate once again quite good agreement bet een results obtained with each geosim for. sway force and yaw moment with increased catter and less satisfactoy agreernent with surge force..
:3.1.5 COmgined Drift and Rudder Angle Eeriments
easurements obtained with combined drift and rudder angles are shown in.
'igures 26 to 38. Differences in absolute measured X1, Y' and N' alUes are apparent in the results obtained with the NMI and Stevens' models Whereas good agreement in t and N' against
for zero drift angle occurred, progressively poorer agreement was found as increased. This was especially notable in the :.Y' méasiirëmënts as shown in Figures 35 and 37 where crossplots = 15° are
shown for deep: arid shallo water.
In spite of the poor agreement between absolute measurements, it is apparent
frOth the Y'. and N' plots in Figures 27 to: 34 that the lppe of the curves obtained from the two models show reasonable agreement.
Agreement between X' values measured with the two models is generally poor.
-This is not altogether unexpected as: jt is these values whidh may be expected to be thot affected by viscous, and hence scale., effects.
3.1.6 Rotating Arm Experiments
Results obtained from the rotating arm experiments are, shown in Figures 39 to 56. The plóttings are axraiiged in two groups; One (Figures 39 to 47) show X'R, R
and N'R for both models plotted against r* (= rL/U) for various drift angles while the second group (Figures 48 to 56) show cross-plots of X'R, Y' and N'R
against for va±ious r*.
It may be.noted'that in the axis system of Figure 5 a negative drift angle is bow-into a clockwise turn; this is normal for most displcement ships in
a steady turn. It will be seen however that rotating arm experiments were also carried out at positive (bow out) drift angles whiOh were almost as large as the maximum negative drift anclês tested. The purpose of this was
two-fold.
to allow for' any major transient behaviour in future simulation models in which large positive drift angles may. be associated with positive rates
of rotation. .
- to proVide sufficient data. to explore the validity of the cubic terms involving combination5 such as v2r and yr2 which are often used in manoeuVring simulation models.
For the NMI model in deep water, it s apparent from the cross-plots at various r* against drift angle that for positive there is little 'variation o Y' or N' whereas major variations are obtained for negative .
However results from the Stevens model in deep water show a different sway force behaviour with at a given. r*. In Figure 49 it i clear that a minimu value of 'R is reached at 50 after which an increase in sway force accompai4es
an increase in at constant The yaw moment variation with at constant r* also differs from that of the 4I mbdel for positive (seeP Fig 50).
It may also be noted that whereas the magnitude of XtR and N'R of the NMI and Stevens models agree reasonably well, at a given and .r*, this is not the case with R The Values obtained from the Stevens model are about half the.
In shallow water the 'R results obtained with the NMI ode1 are interesting. It is seen bycomparison with the deep water values (Fig. 49), that at both medium
(:.5) and shallow (1.2) depth/draught ratios!
th
'R values increase with increasing positive drift angle and decrease after reaching a maximum for decreasing negative drift angle. Indeed at large enough negative drift angles rptary. sway :crce becomes negative. This .mày in part be due .to bloökage effects present in the linear motion results obtained in the towing tank No blockage cprrection has, yet been applied to the shallow ater-esults.Changes of N'R with depth (rigs 50, 53 and 56) are not so dramatic although it is clear that for positive drift angles N'R becomes less negative with decreasing
hIT. Indeed at = 200 and h/T = 1.2, N'R does.in fact become positive.
The increased magnitudes.of X'R, and N:'R with reduction in water depth may also be noted as may the rather- less linear variation of 'R with r* at some positive drift angle as water. dpt s reduced. .
3.2 Free ,RunMng Experiments
Results from the free-running experiments were obtained by analysis of the track 1Ots, an example of which is given in Figure 57. Analysis yielded rates.of turn, turning radii, v1ocity. in the turn and drift:angles. As mentioned in section
2. 2,. only the NMI mode-i could be run free and the experiments were -confined to
-teady state turning circles and pull-outs.
Rate of- turn against rudder ngie for the three water. depths is shown in Figure 58 while Fiur-e 59 shpws.tack speed on thë- turn. -.
It is seen in Figure 58 that good agreement between model and full-scale. measurements of rates of turn are obtained in shallow water (h/T = 1.2) while
12
-particular interest is the fact that the marginal instability noted in reference 1 at h/T = 1.5 is correctly reproduced by the model measurements although in
general the rate of turn of the mode-i was somewhat less than that of the ship for this water depth.
This also appears to be the case in deep water although.. in this case it was not possible. to obtain reliable model resUlts- at rudder angles less than 5° starboard or 10° port. It was therefore impossible to determine whether the margiial dynamic
stability measured on the ship in. deep water was correctly reproduced by the
model. . .
The observed differences between rates Of turn measured on the free model and at full scale may be due entirely to scale effectS, but model aid full-scale thasurement accuracy should also be borne in mind. Some discussion of the measurement problems at full scale is given in reference 1. where it is pQinted out that it was necessary to correct all measurements for the effects of current. No current was present in thea model experiments.
Another difference between the model and full-scale trials was that whereas the full-scale rates of turn were obtained from a spiral manoeuvre the ode1 results were obtained from steady state turning circles, measurements being initiated after the model heading had changed by 3600 and continued until the heading had changed by 7200 after the. initial setting of the rudder to the required angle. It is possible that, Should the rate of turn take some time to settle to a truly steady value, the. spiral tests of ref. I could have yielded rates of. turn which
were higher than those in the model tests.
Speed lOss measured in the turn is shOin to be reasonably well pedicted by the model at least for hard-OVe turns. The expected greater speed loss in deep
compared to shallow water is apparent from the model results in Figure .59
Measured drift angles in a steady turn are shoi itt Figure .60 for the }4I
free,-running model. Although sject to sOme. scatter, the reduction of 'dr4ft angle with reduction ofunderkeel. clearance is notable.
4. Manoeuvring Coefficients and Simulation
4.1 General
It is straight-forward to compare free-running model measurements with results obtained from the full-scale trials. But in order to assess the validity of the constrained model measurements it is necessary to use them in a simulation model the
resu±tB of whfch may thn be compared with both free-model and full-scale measurements.
Clearly such a procedure is as much a test of the simulation model as of the model measurements themselves and as such it allows an opportunity of assessing the suitability of various features of the chosen simulation model. In this section therefore manoeuvring coefficients for a chosen mathematical model are presented and discussed after which they are used to simulate steady turns for comparison with free-model and full-scale measurements.
4.2 Simulation Model and Manoeuvring Coefficients
The NMI cruising speed model has the form (ref. 3):
m*(uI_vIrv) =
XU'2
+ X2v'r' + X3A1c52 + X4v'2 + X5r'2 + X6n'2 + X7U'n' + X8u' + XEm*(v'
+ u'r')
= Y1v'U' + Y2U'r' Y4vhIv'I+ Y5r'Ir'I + Y6n'2 +(Y7 +
m*/2) v'2r'/U' + Y8v'r'2/U' + Y9u1 + Y10r +I r' = N v'U' + N2tPr' + N3X S + N v'Iv'I + N r'
Ir'I
+ N6n'2 + N7v'2r'/U'zz 1 2
4.
5+ N8v'r'2/U' +
N9t
+ N10r' + NEwhere XE, E and NE represent external forces and moments and
= a1r.j'2 + c2n'2 + (l-cL1-c12) U'n' + cz3Iv'-kr'IU'
A2
. 14
-The regressIon model given by equations i) to (3) has been found to represent adequately the behaviour of a range of ship types and has been used extensively in. UK-manufactured ship simulators designed both for training and research roles.
Coefficients, in the simulation pde1.we obtained ii groups using results from 'linear motion' and rotating arm experiments. In all cases standard errors of each coefficient were calculated and these are listed below.. The 'linear, motion' results
showed characteristics which were simil.r. over the-whole drift angle range, to those obtained with other models at NMI. This was not the case with the rotating
arm results however and these. are therefore
discused separtely.
4.2.1 Linear Motion Coefficients.
The 'linearmotion' experiments (resistance, bollard pull, oblique tow, rudder
angle and combined drift and ruder angle epariments) yielded the coefficients
in Table 4. Some coefficients for the Stevens model have had to be estimated and
these are marked.
..
... . . .. .Comparison of these coefficients wIth others .given
n reerpe
show that theyare generally of .imilar magnitude and sign.
The errors given with the coefficients are as much a measure of the accuracy of. the experiments as they are of the adequacy of 'the regression model (equations (1) to (3)) to fit the experimental data. In general it is seen that the fit for
both the NM and Steyens model data is good with one or- two exceptions, primri1y
associated with non-linear terms such as X4v'2 and, y4v'
Iv'
.-The rudder effectivene'ss ( and ) coefficients (obtained from the combined
driftand rudder angle experiments.) show .goo agreement between, the two sets of measurements from each model with the. exception of However the error size in the coefficients from the Stevens model data should be npted;
their lage
size suggests that the 3lv'-kr'I term is not a good fit to the experiment data.
In general however the agreement between results obtained from both models is reasonably good for linear motion and. differences which do occur, notably in
the resistance (X1) some non-linear and rudder terms are not altogether unexpected, and probably not significant when the error bounds a considered.
MODEL COEFF. DEEP
1.5
.1.2
X1-1.75(0.034)
-2.14(0.076)
-4.22(0.010)
-2.16(0.061)
-2.30(0.18)
-.3.22(0.15)
X42.65(1.80)
7.07(2.32)
- .68.4(6.92)
x6
2.21(0.07)
2.36(0.035)
3.05(0.05)
-0.46(0.08)
-0.22(0.084)
1.17(0.086)
-15.7(0.86)
.-17.0(3.7)
-119.0(16.7)
5.14(0.31)
5.74(0.17)
8.10(0.32)
-49.3(4.9)
-0.045(0.042)
-412.0(22.5),
-0.38(0.08)
-408.0(83.1)
-0..25(0.022)
N1-6.96(0.28)
. .-24.9(0.84)
.-34.7(1.89)
N3-2.22(0.09)
-2.22(0.046)
-2.44(0.07)
N4-9.67(1.61)
3.13(5.14)
-43.9(8.51)
N6-0 042(0 003)
-0 014(0 008)
-0 025(0 010)
sTEVEi1s_2.05*
_2.i*
.4.91
x3
-.2.40(0.4.5)
-3.43(0.37)
-2.91(0.59)
0.55(2.81)
.83.7(2.53)
2.6,4(0.04i)
2.82*
364*
X7.0..59(0;04i)
. '_0.3l*'
1.27*
Y1'20.3(1.,32).
-24.4(2.71)
..196.:0(13.9)
8.20(0.67)
Y4-57.1(5.43)
. .-374.0(16.0)
-161.0(82.5)
-0.165(0.005).
_0.2.5*
7.88(O.67).
-23.2(0.4i)
.-17.9(2.15)
N3-2l7('0I.4)
'-2.49 (0.20)
-.2l (0.18)
0.756(2.4l)..
,.93.7(i2.3)
N6-0 042(O 002)
-0 014*
-0 025*
NMI -0.l650.035)
0.190(0.23)
0.2090.38)
0.481(0055)
0294(0.077)
0.484(0.04)
0.Q'.
..
0 152(0 037)
0 086(0 040)
0 052(0 009)
0.3'30(0.033)::.
0.340(0.064)
-0.173(0.014)
k.0.5,60(0.44) ,
05*
.2.330(0.&)
.05*
3.150(1.04)
Q5*
svis
0 310(0 13)
0 136(0 13)
0 092(o 16)
0.452(0.07l)
.0.84W.0i8'
.l.87(0.35)
0.0*
O.O..,
QQ*
0.189(0.028)
. 0.022(0.047)
'. 0.035(0.060)
820.365(0.073)
0.405(0.053)
0.450(0.048)
83-11.91(5.98)
-14.08(12.02)
-19.08(28.7)
k
0.5*
05*
0.5*
Notes ] *Estjmated value TABLE 4
Figures in parentheses are standard errors All coefficients app].y to ahead motion only
16
-4.2.2 Rotary Motion Coefficients
As mentioned above, the rotating arm experiments were carried out with a drift angle range of -25° to 200. This was done to enable the range of validity of the rotary term model: (ref. 3)
XR = X2v'r' + X5r'2 (4)
= Y2Utrt + Y5r' Ir' I + Y7V'2r'/tJ' + Y8v'r'2/U' (5)
NR = N2U'r' + N5r' Ir' I + N7v'2r'/U' + N8v'r'2/U' (6)
to be assessed. In equations (4) to (6) XR, R and are the rotary surge and sway force and yaw moment obtained from the measured data after removal of centripetal and linear motion effects.
Multiple regression fits using equations (4) to (6) were made for various drift angle ranges and for the whole r' range tested (including r' = 0). Multiple correlation coefficients and F values for these fits are shown in Table 5.
It is clear from the multiple correlation coefficients than for -25° 20° ,the
regression model is a poor fit to the R data in deep water for the Stevens model and does not fit the R data in shallow water. Clearly the changes in form of the -curves of
R against in shallow- water are not well-fitted by the
regression model.
The situation is considerably improved by reducing the drift angle range to _150 S 50 and a further marginal improvement is obtained if the range is
further reduced to -10° 5°. However the improvement is so small that it
seems unnecessarily restrictive to limit negative drift angles to -10°. It is therefore apparent that the model given by equations (4) to (6) is valid over
a drift angle range of _150 E 50; the computed regression coefficients,
TABLE 5
Model Item Range Multiple Correlation Coeff. F Value h/T
NMI XR
-25°
to200
0.97996
1404.03
deep 'I0.98146
747.46
0.98730
1100.638
Stevens XR 'I0.89850
261.85
It0 86635
92 52
0.98746
1202.74
NMI XR-25°
to200
0.95261
568.84
1.5
0.62968
18.72
10.93791
208.36
XR-15° to 5°
0.97871
636.5
II0.96660
192.04
II NR0.96547
185.43
XR-10° to 5°
0.98593
765.54
0.97314
187.62
NR II0.97449
197.95
II NMI XR-25° to 20°
0.91122
286.28
1.2
0 64364
20 34
NR0.88806
107.27
XR-15° to 5°
0.95272
280.22
It II0 97073
224 58
NR It0.95272
280.22
XR-10° to 5°
0.96310
288.12
U0.97473
204 69
NR It0.94394
87.91
18 -TABLE 6 MODEL
h/T
COEFF 10 VALUESThNDAD
ERROR SIGNIFICANCE NMIdeep
X2 12.93 0.244 H X5 . 0.66 0.139 H -25° 20 2 11.81 1.136 H y -4.36 . 1.329 H 40.04 3.459 H -41.391207
. N2 -5.49 0.393 H 0.13 0.461 N N7 =20.98 1.198 H N8... .8.9.4... 0.418. .., H STEVENS 7 25 0 320 H 0.07 0.143 . N 2.33 0.551 . H Y5 -0.38 0.533 N 20° 11.60 899 H YB. -.3.03 0.611 H N2 -2.16 . 0.149 H 0.34 0.144 S C N7 -10.49 0.51.5 H 0.. 520166
H. NMI15
X2 62.95 . . 1.97 H H X =1.880.S3
H1108
3214
10.97 :3.832 . -15°5°
. . -232.38 37.183,. -129.53 ' 1L34.4 H N2 -8.76 1.4$ H N5 2.04 . 1.767 N N7 -66.59. .17.147 H N8 25.23 5.23 H, 1.2 68.15 3;074 H X5 -0.64.. 0.928 N -15° 5° Y.2 14.73 4.641 . H Y5 28.13 5.522 H -473.50 53.707 H -172.34 . . .16.422 H N2 -13.46 . :- 2.i45 H N5 6.15 2.553 . S N7 -82.63 24.825 H N8 20.78 7.591 'SIn Table 6 the significance of each term has been obtained from its 't' value, values of significance being assigned on the following scale for the appropriate degrees of freedom.
H: Highly significant 0.5% significance
S: Significant 2% to 0.5% I'
N: Not significant
Comparisons of coefficients obtained for the Stevens and NMI models show good agreement on the whole except for the highly significant Y2, Y7 and Y8 values for which the values from the Stevens model are much smaller than those from the NNI model. This is simply a reflection of observations made above regarding the model measurements.
It is apparent from the Table that most terms in equations (4) to (6) are highly significant for the 'Esso Osaka' hull form. The exception is N5r' r' which is consistently shown to be of low or negligible significance. This does not mean of course that it would hot be significant for some other hull form.
The terms
Y7v'2r'/U', Y8v'r'2/U', N7v'2r'/U' and N8v'r'2/U'
are all significant or highly significant with the two sway equation terms being consistently highly significant.
4.2.3 Remaining Coefficients
All of the coefficients in equations (1) to (3) have now been determined from the constrained model experiment results except for the acceleration terms
X8u', Y9v', Y10r', N9v', N10r'
These are usually determined by inspection or identification from comparison of simulation results with free model transient manoeuvres such as pull-out or zig-zag manoeuvres. Assumed values, based on model results obtained previously at NMI, were used in the following section.
TABLE 7
It is also apparent from the magnitude of the C values in Table 7 that the increased directional stability in h/T = 1.2 is correctly predicted by the constrained model results.
Drift angles in the turn are apparently well-predicted (where it is possible to make a comparison) except that those measured on the free model at hIT = 1.2 are significantly smaller than predicted.
Loss of speed in the turn for both free-model and ship are generally quite well-predicted although once again the greatest discrepancy occurs at the
smallest h/T value.
Predictions of the transient effects associated with entry into a hard-over turn are compared with full-size measurements (ref. 1) in Table 8:
TABLE 8 h/T (Y 2_m*).l03 Y i.l0
N 2l0
N .lO3 C.103 -6.43 - 15.7 - 5.49 - 6.96 41.44 1.5 -7.16 - 17.0 - 8.76 -24.90 -29.36 1.2 -3.51 -119.0 -13.46 -34.70 1479.94 RUDDER h/T AT 900 HEADING CHANGEADVANCE (m) TRANSFER (m) SPEED LOSS%
meas. sim. meas. sim. meas. sim.
350 350 1.5 1.2 1.5 1.2 1005 915 1190 1015 990 1180 d 946 999 1010 971 967 971 310 385 555 360 405 705 458 612 631 463 573 582 -35 32 26 33 33 35 36 38 38 36 41 41
- 22
-In general it is seen that while the advance t 90° heading change is predicted. to within 2-10% in deep and medii depths (15-17% in h/T = 1. 2), the transfer
is generally predicted no better than to about 14% of full scale with discrepancies of nearly 60% in one case. This direct comparison between a full-scale and
simulated mafloeuvre apparently reflects the fact, noted above, that model and simulated rates of turn were lower than observed at full scale. This may be a genuine scale effect and, in conjunction. with discrepancies between.full-scale
and model prediction in speed loss and drift angle, combine to produce the differences apparent in Table 8.
5. Genéral DiscussiOn
It has not been the purpose of this report to provide any comprehehsive comparison of model simulation and full-scale results, but rather to 'present the model data, discuss it and compare sorne limited simulation resu1t with full-scale measurements
from reference 1. Further comparisôn between simulation and f'Jil-scale must clearly be made before the magnitude of any scale effects can be decerinined and, naturally, this rémàins to be done for the zig-zag manoeüvres, coasting and accelerated turns described in reference 1.
However, it is significant 'that the simulation model, using Coefficients 'Obtained directly from constrained model experiments, predicts free model behaviour ('at
least in steady turns) rather better than full-scale. This suggests that the form of the mathematical model given by equations (1) to (3) adequately represents the free-running behaviOur of the physical model from which it was derived, On the evidence given above it does not represent certain aspects of full-scale behaviour quite as well. This discrepancy may be'descrbed as scale effect and may be due tq:
- viscous scaling 'effects -existing between model and full-scale behaviour.
- a form of mathematcalmodel which is inappropriate for full-scale. This may be special1y true of terms describing rudder beha'iour in which viscous effects are combined wjth the effect of using model - rather than
- errors in model and full-scale meàsurément. These have been given above for the model-derived manoeuvring coefficients and it is clear that some
have large errors and .theréfo±e -:Ooüld be 'adjusted to 'iniproie the ageeinent
with full-scale.
- other effects. Mong these may be numbered blockage effects on the linear
motion cäefficietit -ho biockaqe cOtréction was applied tO the data. It may also be mentiOned that asirnulation model is only as goodas the
understanding àf.rthè physics of ship behàviour in deep and shallow water will allow. It is Ossib1e that' a better uderstanding of shallow-water
effects (in particular the problems of scale) will allow improved simulation
models to be developed. ' '
-It is clear frOm the donstrainêd model results that In bOth the linear and rotary motion experiments significant differences between some of the NMI and Stevens model results existed. '- These were hOwever balanced, to -a certain extent, :b
areas of substantial agreement. These areas of agreement and difference are reflected' ih the' manOeuvihg OOëfficieht in Tàblès 4 and 6 with perhaps the most 'notable disagreement being Obtained
wi.th
ome'of the rotary terms. It. would appeartherefOre that model size has sotheèffect on the results, but again the reasons for this axe not altogether'cleàr-cut. For example, viscous scale effects on a small model may well be wholly Or partially offset by a reduction in blockage
effects. This in turn may be óffet by' problen ih'maintai'ning measurement accuracy tqith' the smaller forces obtained ith small models together with a greater possibility with such models of a greater tendency for laminar flow (see Table 3).
It is clear therefore 'that further iok remàihs tO be done in the analysis of 'the data presented here and this will fall ubder the following main headings:
- investigation of' 'blOckage effecti
- presentation. and analysis of linear motion data' obtained for drift angles
in' excess of 250. Results (not presented here) have been obtained, with
both the NMI and Stevens models, with linearmotion having drift angles
0 in the range 0 180
-.24 -.
- further comparison of simulation and full-scale results for zig-zag, accelerated turns and low speed manoeuvres.
The results of these further investigatibxs will be presented in due course.
6. Conclusions
Two geosims.of the 'Esso Osaka' have been. the. subjecs'of' a series 'of constrained and free-running experiments to .co,llect data on their manoeuvring behaviour in different water depths for comparison with full-scale measurements. As a. result
of thi study the follOwing tháin conclusions have emerge4:
i) Results obtained in constrained model experiments using 3. 536m (4I) and
1. 625m (Stevens) long models showed areas of agreement together with significant areas of disagreement. The most notable disageemen'was in the measurement of the' rotary sway force coefficients Y'R whose magnitude in deep wate was much less from the small Stevens model compared to the. ti model.
ii). Free sailing, results obtaitèd wi,th the NMI model gave the same qualitative
steady turning' behaviour as the ship. While the. steady ra of turn was only moderately well-predicted in.deep water, 'aqreement between the free-sailing
model and ship progressively improved as watr depth.was reduced...
Changes in' controls-fixed directional stability wh 'water depth, observed on the ship, were correctly represented by both the free and constrained NMI
model results. . . '. ' ,.
Simulation of the steady turn'tesults, made using the NI cruising speed model, agreed reasonably well with results from the NMI free-sailing model.
The transient 'behaviou± of the simulation model at the entry to 'a hard-over turn showed reasonable agreement. with full scale advance (at 90° heading change), poor agreement transfer, and reasonable agreement with speed loss.
There may be blockage effects present in constrained model results obtained
ith large ditanqiès and linear -mOtion in a towing tank.
yiii) Further analysis of blockage effects, large drift angle. results arid transient Motion is required.
7. References
1. cRANE. c L 'Marioeuvring Trials of 278,000 dwt Tanker in Shallbs4 and Peep Waters' Trans. SNAME vol. 1979, p.
MILLER, E R: 'Status Report on a Model-Full Scale Correlation study Based on the 'Essö Osaka' Manoeuvring Dàtà' 19th ATTC, Michigan, 1980.
GILL, A D: 'The Analysis and Synthesis of Ship Manoeuvring' NMt Report R90, October, 1980.
GERTLER, M: 'A Re-analysis of the Original Test Data for the Taylor Standard Series'. DTMB report 806, March. 1954.
SCHLICHTING, 0: 'Ship Resistance i±i
Water of Limited Depth - Resistance ofSea-going Vessels in Shallow Water' Jh±buch der STG,
vol. 35, 1934 pp.127-148.
GILL, A D: 'The Identfcation of Manoeuvring Equations from Ship
Trials Results' NMI report R3, August 1976.
7. COMSTOCK, J P (ed) 'Principles of Naval Architecture' SNAME, New York, 1964, Chapter 8 by P Mandel.
26
-8. Acknowledgements
The authors gratefully acknow1edge theassistance of Messrs. G L Taylor,. G Meek, and Mrs J Salter Of the Hydrodynamics Division., NMI Ltd. Special mention is made of the late W H Sims who carried out much of the experimental work on this - his last - project It is hoped that this work will serve as a memorial to him in special recognition of the contribütion he made to the study. of manoeuvring in NMI. . .. . .
moulded beam
linear stability criterion
block coeffiàient
midship section coefficient prismatic coefficient
propeller diameter
Froude Number = Ui i4L Froüde Depth Number = UI gravitational acceleration
water depth Izz/½pL5.
rotary inertia in yaw
lever arm between origin of axes and ruddêr length between perpendiculars
rn/½pL3
ship/model mass shaft rpm
reference rpm
n/n0
mean face pitch
yaw rate
rL/U
rLp/U0
at-rest draught
track velocity = V'U2 + V2 reference velocity
surge velocity sway velocity U/U0
v/U0
external surge and sway forces and yaw moment XR,YR,NR rotary surge and sway forces and yaw moment
drift angle rudder angle
A A .rudder coefficient modification parameters
P water density
trim angle
denotes non-dimensional quantities mainly: forces w.r.t.
½L2
0 and moments w.r.t.½PL3UO2
Cm Cp D F Frth g
IzzI
Izz m* U 'U0 U! VI XE,YE,NEF2
-T&i
11
t
I,
IL_________
IL_ I IL
91/.2UI
11_ 11
1
12 m 4 34 rn28m
20 m7-5
21 97-mLWL
I-AP
1/4
BOW PROFILE AND WATERLINE ENDINGS
0 SCREW w2 as STERN ARRANGEMENt SCALE(m) E 10 -I-1/2
I
S
DRIFT ANGLE VANE
HEADING GYRO BATTERIES ETC ULTRA-SONIC TRANSMITTER
'ESSO OSAKA' MODEL
EXPERIMENT TANK
DIAGRAM OF FREE RUNNING EXPERIMENT SET UP
ULTRA SONIC R ULTRA-SONIC
PLOTTING
SYSTEM TELEMETRY Rx ETC RADIO CONTROL Tx TEKTRONIX I 4051 1PAPER TAPE PUNCH
CHART
AXIS SYSTEM AND DEF1NITIQNS
(POSITIVE DIRECTIONS. ANGLES AND ROTATIONS
DICATED)-2 -.4
-!ES.ISTPNCE
.ö4
A
ESTIMATE-i
N-a
1 DEE P] h
/ T -1 5______
hIT-li
4 . 16BIJLLq!D PULLS
24
a
DEEr. NEF VoD ar. VMI
V LV. -STO V .2. 550 X 0 lEEr. 'aec STEVENS BOLLPIO PULLS Y' (1 DEEP. EF ND42 5PM. MIS! to a IS. co -0 1.2. 580 0 0EEr 080 STEVENS BOLLRD PULLS N' '0 '0 0 DEEP. Er-sso=4?o-prM. MM! DI (I LV. SIO (1 .2. SaD 0 DEEP. '000 STEVENS
DEE? WRTEL, y'
O RUIDDE! RNCLE. NM! FWOEL
U STEVENS
DEEr WPTEt,
ai
10 15 20 25
h/T = 1.S,
>(-25
-20
-15
0 UODE
RNLE. NMI t1OEL
El 0 STEVENS
15 20 25
DRIFT RNGLE
H/T =
0 STEVENS
jo
:0
-25
-20
-15
-10
S 5 10 15 20 DRIFT GLE0 UODE RNGLE. NMI M0EL
0 STEVENS
I-l/T
= 1.S,
NF1/T= 1.2w
X
18x' *O**3
a
a
0
10iS
20 250IFT flMCLE
h/i = 12,
I
pC UDER RNGLE. NMI MODEL
0 STEVENS 10 15 20 25 DRIFT RNCLE
0
0
FIG. 15.
h/T. = 1:2,
o
10 15 20 25
DRIFT RNCLE
-40. -30. -20. -10. . 10. 20. 3O 40
RUDDER ANGLE
0
DEEP,
x
0
0 DRIFT .qNGLE. . NMI MODEL
0 STEVENS MODEL
0
0
-40
GDEE?,
5-'f'
*(o**3)
G 4 ---I
-20 30 40 R1JDDE ANGLE
FIG. 19.
-40 -.30
.20
10
ii 1.0 30 - 40RUDDER RNGLE
0 DRIFT RNGLE. NM! MODEL
W 0 STEVENS MODEL
UEEP,.
NH/T =
H/T = L5,
I
T' *(I0**3) 4 3 2 I -40-(1
2C) -!0 ]0 20 30 40 U00ER NCLE III lii Lii 5-0 DRIFT RNGLE, WHI W0EL
E!J 0 STEVENS !WOEL
a'
a'
FIG. 21.
-2
H/T
1., S,.
I-
- I - ___--40
--30 -20-10
1.5
-1. 5
I i__: I 20 30 40 RUDDER ANGLEIII
-40 -.30 --20
10
- 10 20 30 40UDDE N.GLE
--1
D
0 DRIFT PNGLE. NM! MODEL
0 STEVENS MODEL
H/T
L2.,.
I
I6 'r' *(IO**3) .;
-40
0
H/T =.L2,
'.4-30 .4,. X''*(1Oc*3)
20
10
1 10 20 30 40 LJDOER RNGLE-.2
1.4'
t1EL
-40
-30
--20-10
10 20 30 40 RUDDER ANGLE..0 DRIFT RNCLE, NM! MODEL
0. STEVENS MODEL
H/T =
D
Vø.
DEE? WPTE,
-io
a .iS a-zo
o STEVENS -5 a -30 a-is
-zo
a 10 ZD 30 RUDDER qNGLEx
DEEP WRTE, 1'
18 'rti0''3)
16 14 12 i C oDRIFT PNL. NNI 111DfL
-s
-0
-Is
-20
0
x
x
STEVENSFIG. 2.
0
x
-20
10
10 20 30 RUDDL RNGLEz
x
2:
A
DEEP ,jpTE
''
2:
A
-15
-20 sTEVENS0'
-S-10
2:
-20
100
2:
A
0
2:
A
.z0 33 UD0E NCLE1.5::
X'
0 20 30-40
-10
IUDOE RNGLE 0DfT PNGLE.
ii
-s
-10
x
-is
ao
a 5 a a t:-io
a a-20
Nt-Il 1OEL
ST,Vr4S
0
0
FIG. 29.
-3D cD 20 30 RUDDER RNGLE STEVENS
-10
-Is
-20
0-5
-10
-15
-20
0
x
z
x
14N 'iO31
-30
-20
-10
0 DRIFT GLE.
4r1I tlDEL
-5
0
0
m 20RUDDER NLE
FIG.. 31.h/T = i.E.
N I-10
-15
-20
0 STEVENS-5
-10
-Is
-20
qc 10 20 10 U0DE ANGLE STEVENS
0
x
Ih/i = 1.2,
Xh/T = 1.2
0DRIFT P.NGL. JWJ
IWDEL-5
-10
-Is
-z0
0-5
-I0
-]:5
-20
STEVr'S
FIG. 33.
hIT = L
-10
-Is
-z0
o-s
-10
-15
-20
STEVEt'ISz
ib
,...2O
3D RUflDE qNCLEDEEP WPTE,
-
UCDE PNGLE.. NMI !1OELIs.
-15
STEVENSx
is
.4
-15
stvs
FIG. 37.
.
-5
UDOER qcLE. NtII NaDEL
is
STEVENS
-IS
STEVENSOLICC QtfCCU CCfl--NLfl--NN,J I I I I EJ
MS''
M N,X N N U, 419M
'dO 0 0 N9O
E N 8 8 -fltflO.-.NLflNN
ClLflClU) 9 9--N
N N N9
C-N FIG. 39-'
fl 'J b48
1d'M
0 oi
--'E'
JN N'
N N IJ U, -U, N88
ee
N N EEB
ThJ 'DEEr W'PTE'I,
1 .2
-s
0
IflI!FT
GLE., STEVENS MODEL
S 13 Is 20 -ID Is -20 -ZS m 0 '0
x
x. V 'b. cix
x
' 0 En 0 ci A En A .5flEEr Wfl TElL
0DRIFT pILE. Mlii MODEL
S 10 15 20, -10 -15 -20 -25 0 -.2 4 -..6 S 4.5 a 3.,5 3 2.5 (
(13
x0
22 20 1 6 16 14 12 *(Jfl*3)z
8z
z
4.
2I
0.--3.
DELF W-T1E,
"H :K D!FT NLE. TiEVE.'1S MflEL w a NR *(l0**3! 1 --5 - 9-DEEr WRTEI,
N 2z x
x
.0DRIFT PNGLE. NM! MODEL
S .10 X 15 ID 20 -5 -m -ia & -IS Z -20 c -25-S
x
18 --6 -32
1.1/-I
=
1,
X!
.4
10 15 20-5
-30
-is.
-20
-25
.6
0
0
XR15
-12 9 S.(10$31
0
0
x
0
0
0
x
20
is
-S-Ic
IS
20H/T = 1...S.
1i
0
0
0
OIFT PNLE. rIMI MODEL
5 10 :15 zD
.5
-.10
-.L5
-z
FIG.. 43.
30
-'r103)
25
-0
0
h/T.= LS,
NR:
0
10x
is
zo
-s
-ID
-IS
X
-20
-0
0
3
15
-12-6
--9 12h/T
2'2.,
0
4
-
.4
x
I
00JfT PrIGLE.
jj 1WDEl.
5 4 4 .1 10Is
20
.-5-10
-45
-2 D -2.5.6
AA
AFIG. 45.
2 N!
M0*3)
tt/T
=-1.2,
N .-10',
1s
. _z0 c25
. 0 OR!T-R!'lGLE.: NM! MODEL s 10 -is
20-x
x
FIG. 47.
--20 -IS -U) -2.5 1,5 0 1' lB x DI 2 lB
x
lB 2 . l3 9 STEVENS I00EL DI .!E .21? X .255 CD ID lB 0 !.S 20 25 fINGLL DI -2S -20 '-15 -10 O'EEIwfrrE
X 0 ID 0 .ZG R. MM) MODEL ED .36 £ .44?x 0
788.0
0x
-x 0 DRIFT RNGLElEE' WqiE
J35 STEVENS MODEL w .iss -.2-I? X .25 .555 < .4S DEEI WP1EF.iI
--25 --20 .28G . NM! MODEL W -. -' .q4?37
cn 78 10 IS 20 25 091Ff PNGLCIJEE!
N -2 -!5 .lO --Sx
J 'zi R. STEVENS !11DEL flfl?
X .23S D. .353 DEELD WPT-EI, NM :zaG M*. NM! MODEL In .3 .447 X .637 Q7a
3D IS DRIFT0
0
0
t-1/T
= 1.S;
XR-25
-2D -1.5-iD
-xgro'-3)
.15 9 6 3.287
*.
NtlI MODEL.355
.44?
X
0
0
0
K
K
I - I 1O 15 20 25 DRIFT RNCLEFIG. 51.
K
-12-s
D
z
0
h/T = 1.5,
'r
.36
A
.44?
X
0
.788
0
0
A
A
x
0
A
A
0
0
X
x
A0
0
A
x
0
0
25-0
-15
-10
10 15 20 25 DJFT PNGLE-S
-iD
A
-1.5A
-20
it
30IiD3)
x
250
0
0
x
20x
is
-25
-20
-15
-10
-S
5 10 15 .20 25K
K
C
C
K
C
0
. NM! MODELD!FT ANGLE
x
x
C
C
FIG. 53.
0
C
C
x
C
C C 10 IS 20 2S DRIFT NCLEIs
)(R(iO3)
C
.12x
x
9x
4
x
x
4
C
64
.44?
.i32
h/T = L2,
XRx
H/T
.o.
cD S 0 'rR(1O3)
40 .1 -] 0-20
-30
-40
.282
FkNM! NDEL
.3S
.447
XG3?
cD:7. ..-..
I--- -5 10.r15
20 25D!f1
NCLEFIG. 55.
H/I
12J CK
2 T.Ng *(IO*3)
-2
1Q-14
- I-.447
..x.
. 1FT RNCLE III0
C
TYPICAL RUN PLOT
RUDDER - 200 P
DEEP WATER
RUN NO 14
DEEP WATER
+ NMI MODEL MEASUREMENTS
- FULL SCALE
SIMULATION (NMI MODEL)
+