7X,1(41.4 dt/fr,
9.
Calculations on the Steered Motion of a Ship under the
Action of External Forces
(Part I)
Coursekeeping and Turning of a Shipin Uniform Wind and
Flow-Akihiro OGAWA*, Member
From J.S.N.A. Japan, Vol. 126, Dec. 1969)
Summary
Considering the possibilities of solving the non-linear equations of motion numerically on
a digital computor, the author contrived a method for numerical calcuration of the steered
motion of ships in uniform wind and flow.
The aerodynamic forces and moments and the longitudinal hydrodynamic force were taken in as the intermittent functions of relative wind direction and the Froude number respectively, and were interpolated at need. The so-called rotary derivatives were decided by a least-squares method, up to the third order of transverse velocity, turning rate and rudder angle, from the tested points at various values of the parameters. The equations of motion were described on the absolute motion of ship, and the external and inertia forces and moments caused by the relative motions were calculated at every small time
interval and integrated.
As an example, calculations were carried out on a mammoth tanker regarding the re-quired lowest speed and the course stability in a straight course and the turning behaviours
in wind and flow. Results of the calculation on the turning characteristics in calm sea were compared with the tested results on a free-running model and on the actual ship.
The following conclusions were obtained concerning the method of the calculation and the calculated results on the steered motions of a ship in wind and flow.
The non-linear equations of the un-steady motion of a ship can be calculated numeri-cally on a digital computor.
The required minimum speed and the course stability in a straight course within the limits of definite rudder and drift angles can be calculated.
In some cases the course stability index has a periodic solution.
At the above-mentioned minimum speed, the ship tends to be course-unstable main-ly in case of following wind, though the stability is improved by the higher ship speed.
The effect of wind and flow change remarkably according to the loading condition of ship.
The average direction of the macroscopic " drift " of the steadily turning ship does not necessarily coincide with that of the uniform wind or flow, and the average speed of the " drift " is smaller than that of wind.
tically, since the equations of motion usually
1. Introduction require non-linear treatment of hydrodynamic
In general it is very difficult to solve the forces and moments on the ship. As is well
unsteady motion of a steered ship analy-
known, however, by the application of an 'lc Ship Dynamics Division, Ship Research Institute, electronic computor, there is a possibility of124
Calculations on the Steered Motion of a Ship under the Action of External Forces 125
solving even a very complicated equation
without reforming the formulae.
Such amethod of numerical calculation can of
course be applied to that of ship's
manoeuvr-ing motion as, for instance, reported in 1).
In such a high speed numerical calculation
the formularization of the forces acting on the ship is not necessarily needed, and
ac-cordingly the external conditions such as
wind forces and so on can be freely taken
into the calculation.
By these methods a
higher accuracy of the calculated results can
be expected if the applied method was
suitable, and some applications, for instance
to the calculation of course-expectation for
preventing collision, can be thought of.
On the other
hand, though the
hydro-dynamic forces on ship's hull have been
investigated in the forms of wind force
coef-ficients and manoeuvrability derivatives by
the experiments in wind-tunnel, rotating arm and oblique-tow tests and/or forced oscillation
tests using restrained models, the results of these investigations do not seem to be fully
utilized by reason of the difficulty of the
method of applicational calculation. The
effect of wind are usually considered and
discussed in relation to the course-stability or coursekeeping ability as, for exmple, by Nakajima2), Eda, or Welnicki4), where the wind forces have been taken in under some
assumptions for the convenience of the calculations.
Considering the above state of affairs and
a favorable circumstances that the author
could use an electronic computor at will, he
contrived a method for numerical calculation
of the steered motion of a ship in uniform
wind and flow without reformation or approxi-mation of the formulae. The report describes the method of calculation and some examplesof the calculated results on a mammoth
tanker.
2. Expression of Motion and Method of
Calculation
2.1 Coordinate Systems and Symbols
A coordinate system as shown in Fig. I
was adopted according to the conventional
means which has been utilized generally for
the analysis of manoeuvring motion after
Hovgaard". Only the transfer and rotating motions of the ship in the horizontal plane
were considered. In order to avoid the con-fusion, some symbols were let coincide with
those in computor programs, regardless of
the usual ones. The applied notations are shown in Table 1, and the angles and direc-tions in Fig. 1 show the positive values.
Fig. 1 Coordinate Systems
Table 1 Nomenclature
0-X, Y Coordinate system fixed in space
Xo, Yo Position of C.G. of ship referred to
0-X, Y
00-x, Coordinate system fixed in ship, origin
at C.G.
UF, Absolute speed and direction of uniform
flow
UB, cbB Absolute speed and direction of uniform
wind
U, /3 Apparent speed and drift angle of ship
14x, up x- and y-components of U (= Ucos
Usin j3)
Turning rate of ship (=;)
Heading angle
,av Relative ship speed and drift angle to
water
vx, vp x- and y-components of V (=- Vcos tit,
126 Akihiro OGAwA
E, F, G
Ea FE, GE
Ew, Fw,G , t
Relative ship speed and angle to air Course angle (=0 19)
Rudder angle
Ship's mass and mass moment of inertia Added mass components and added moment of inertia
x- and y-components of force and moment on ship
Hydrodynamic forces and moment below waterline
Aerodynamic forces and moment above waterline
Propeller thrust and thrust deduction
coefficient Time
Distance of pivoting point before C.G. Ship length
2.2 Equations of Motion
The equations of planer motion of the ship
can first be expressed in an arbitrary
coor-dinate system moving with the uniformflow
as follows:
m+mr)13x(m+)novur=E
G=Ga+Gw+Gai,
The inertial terms were followed after the convensional expression as, if necessary, described in detail by Motora', or Watanabe.
Since the relation between the absolute
and relative motions to water are shown by: vx=ux+ Up cos (0
vyuv+ UF sin (OF 0)
z)z---.1tx U, sin (0E-0)S
/),-= tiy- Up cos (0,-0)S
Eq. (1) can be rewritten as: +
(111+ my)ityF,.r=Fy
(L+ I)i' Ggiy= G.
Ex= Err + +E(1 t)+E(m + m 5)v 5 (m + mr)Up sin (OF g5)Ir
Fy=FH+ Fm [(m+mx)vx (m+my)
(5)
Up cos (OF cb)Ir
G G Gw G,)U p cos (0 q5)r
for the convenience of following calculations. 2.3 Expression of Forces
Among the terms in Eq. (5), FR and Gil
were expressed by the third orderpolinomials
with the derivatives obtained from rotating
and oblique tow tests on a restrained model, as:
Fa= Fi+ Fry,' + Frr+ F03 +
+ Fr,r2 + F.52+ Fo,v 5r + Fro ro E,y5vy+ F.,yv53+
+ Foaa + Ftn,rvy'r+
Frror2a-Fooyii2vy+ yr + Froor52 Fom3v52 + F0,3v yro
= G1+ Gyvy+ Grr+Goo+ Gmv52
+ Goa' + Gorvyr + Grora
GoyOvy+ Gmyvy' + Gm-r' + y2 r + Grrar,o + Goa,,a,v+ GOD,.v 5r2 + Grr,oral
+GomOv + Gyrovyra
( 6 ) Since the function Eft to vy, r and ô had
not been decided, a resistance test result was applied as a function of Vi. The resistance coefficient was represented by an intermittent
function of the Froude number, and
inter-polated for a certain yr value at need, or
extrapolated for the lower speed range than
the lowest tested
point by a
quadratic formula. For ET and 1-t a similar method could be applied. Here, however, 1-t,effec-tive power and propeller efficiency were
assumed constants for simplicity,and a
relation:
ET(1 t)v, = (E110+ Ewo)vxo ( 7) for initial values Eno, Ewo and vA in straight
ahead condition of ER, E5 and yr was
as-sumed to be valuable.
For Ew, Fw and Gw similar intermittent functions as E11 were applied using cubic
where: expressions of pw when interpolations were
(m+m5)z3,+(m+mx)v.r F ( 1 ) -=G where: E-= Ea + Ew + ET(1 t) F= FFI+ F w Ft ( 2 ) ( 3 ) ( 4 ) (L.+ + + + + + Grxr2 G60003 ( W, Pw m,, P2x,
needed,
As the calculations were carried out on the
motion relative to the ground, conditions of
external forces were given by UE, OF, U8 and II, and V, pv, W, pw etc. were calculated at every moment.
2,4 Method of Calculation
The numerical integration was carried out by an Euler's method. The ship motion was
calculated from Eq. (4) as following:
k 1) Linear and Angular Accelerations
V) (n+ iny)G+GtFu_
7
(in +in AL+ hz) FiG0 Linear and Angular Velocities,
(2)
Calculations on the Steered Motion of a Ship under- the Action of 'External Torce's 127
t-it U7(t)=142.(0)+ E a.x(r)At t - t try(t)= u(0)+ ,=0 t-KO= r(0)± E r(r)At ,=0
( 3 ) Position and Orientation
Table- 2 Principal Dimensions
3. Employed Data for Calculation
A 'mammoth tanker T-Maru was Selected as the object ship for the calculation, by the
reason that many experimental data were
available on her. The principal dimensions are shown in Table 2.
The model ship in
the table were employed for the experiments
on FH and GH by rotary tests., which con-.
t-Je
X4t)= X0(0)
, 0
lux(r) cos 0(r)--uy,(r) sin (p(r)1At
1-Jt Yo(t)= IT0(0)+
r=0
1u2(r)..Sin0(7)+14(7)cos 0(z-)1,At
I-Jt
OM= 0(0),+ E'r(r)A1
7=0
( 4 ) Drift angle and Pivoting point
p(t)=-ltan-'
uv(t).
ur(t) p(t)= U si13)(t)In the computor grogram, both non-dimen-sional and dimennon-dimen-sional expressions were
ap-plied in order to decrease the number of
calculation times to let the accumulated
er-ror as less as possible.
(10)
Condition Full Load Ballast
Ship
,
' Actual Model Actual Model
Length b .., L (m) 290.00 1.5000 1 Breadth (m) 47.50 0.2457 Draft at midship (m) 16.08 0.0832 7.40 0.0383 Trim (%,), =0.1 +1.33 L. c.. b. '(rn) =7.32 =0.0379
1.20
0.0062 Block coefficient 11 0.805 Displacement 4 (ma), 1 178,114 0.0246 ' 95,025. 0.0131 Prjoe'cted areas above waterline .(m2) Front 0.0275 00343 Side 0.0859 a.1386 8) in+ nix I( z+ hz)Fy+ Fi(in + in5)(1x+ FiGt)
iiu(r)At
+
r(t) (
128 Aikihiro OGAWA
sisted of rotating-arm and Oblique tow tests,
and on Ew, Fw and Giv by tests in a tank
with wind-blower at Ship Dynamics Division,
Ship Research Institute., The rotary tests
were carried out at the model self-propulsion
point by the speed corresponding to about
13 knots of the actual ship. The derivatives
in Eq. (6) were decided by a least squares
method simultaneously in a non-dimensional
form from all of the measured forces and
moments, after being subtracted the
centri-fugal force component of virtual mass_ These
derivatives are shown in Table 3 F1 and GI were put to 0 in the calculation.
EH was derived from a resistance test result
on a 6.5m model at Mejiro Tank. That of
the full load condition are shown in Fig. 2. As
the tested ballast conditions were different
from the calculated one, the resistance curve, was estimated by interpolation,
Table ,31 No"n-dimensional
Ew, Fw and Gpv were obtained from the
original test data by Tsuji and others", being non-dimensionalized with the sea water density for the convenience of the calculation.
These are shown in Fig. 3.,
On the added masses and so on, m5 and
./z. were derived from a mean value of the
test results on a 2m model by Fujino",
and L was let coincide with that of the
I
Fig_ 2 Resistance Coefficient of ship (Fun Load Condition) Rotary Derivatives
* Variables are taken in the non-dimensional form
Variables.* FRI1 -9pL2U2`x 105_ 1 GE/1-p/..3 U2 X 105 2 FuE 1 _ 1
Ballast Full Ballast
11. 1 10.37 29.95 -0.32 -8.18 ,yy 1 -.2,041.63 =4,197.31 =589.28 -821.19 I 841.79 393.04 -371.30 =172.37 a I -527.27 -416.00 209.56 176.98 I v7,2, r2 1 -48.93 -141.03 -68.19 -145.23 27.77 -83.64 0.29 -0.46 42 1 112.35 -69.63 -65.06 25.96 yvr 90.79 40.55 46.80. -24.15 ro -70.72 23.16 51.05 -13.09 ,Otry 27.09 -131.91 I -17.23 48.65 yin -4,825.21 -1,996.82 132.96 =11.91 rt -511.32 1 -169.45 11 5.108 -5.07 (33 vy2r '1 -150.78, 2,246.26" 19511 1 1,664_77 106.22 -1,647.93 -80.56 ----854.79 r2o -2.02 I 5.68 119_81 12.97 32vy -35.44 416.17 142.41 -160.44 vyr2 -2,996.94 -1,014.31 1,102.73 285.30 Mt 81.38 -80.28 -71.28 12.52 avy2 -596.27 1 -259.04 447.41 140.01 vyro 3,166.84 1,798.88 1 -1,583.73 =801.79' 0.010 -K II 1 it 11 IT FULL LOAD, 4:120 0.15
FROUDE NUMBER, Fn VArgt,-,
010
FH
r
Calculations On the Steered Motion of a Ship under the Action of External Forces 129
presented in Table 4.
4. Calculation on Straight Ahead- Condition
ill.ONGIT. FORCE
Fig. 3 Wind Force and Moment Coefficients (Non-dimensionalized with sea Water Density ps)
model, mx was :estimated from Motora's
chart"), and mx, my and Izz of tke ballast
condition from both the chart and those of the full load condition. .Since there were no
avail-able data on L of the ballast condition, the
same non-dimensional value of the radius of
gyration to that of the full load condition
was applied. Ft and Gi of the full load
con-dition were also based on 9). However, as these values, did not make any difference to
the calculated results, those of the ballast
condition were put to 9 .
These values are
Table 4 Added Mass Coefficients and Radiiof Gyration
41 Limiting Condition
As a basic state, the straight-ahead
condi-tion of a ship in uniform wind and flow was
considered at first.
In this case, the ship
advances in a straight course with a
combina-tion of drift and rudder angles, which are
usually smaller when her speed is higher
and increase rapidly with the decrease of her speed.
In general the problem of course
keeping quality in wind, when there are onlywind as the external force, is treated by the conception of the necessary rudder angle to
keep the course for a definite value of UBIU.
Here, from another point of view, the
mini-mum ship speed required to keep the straight
course within limited values of both rudder and drift angles were defined as the lowest speed navigable in the straight course. As the limit angles +10° both were chosen con-sidering that the ship was a mammoth tanker,
and that actually
the rudder angle was
ceaselessly fluctuating around its mean value, and further that she could change her course
by steering from that initial condition.
30
-30° -20° -10° 0 10° RUDDER ANGLE 6
Fig., 4 Example of the Solution of Eq. (12)
iN I LI L u , - ...
WI
t
5 ' .1 . - 0 Y -UF.-.12 Ikn tit=20°' UB .60 kn tpi3 =1140?' i :.°
k
IL
- ''. LUE,FZ661kn 1 c, ,' Gnr0 h BALLAST C,ONDL.Condition Full load Ballast.
Added mass
coefficients,
m,Im 0.060 0.035
mvini 0.810 0.500
Radius of gyration c011, 0.282 O. 282
Added radius of gyration,
A-,..,/i... 0.205 0.150 Coupling term coefficients Fi 0.615 x 10-3 0.10 . GA) i' ,OL 100 x 10-4 0.0 20° 30° 3r 60. ao°
WtNch PREC11 ION if3iw
I ESCI 30° 20° UJI Er: 10 -20 0.6 -0.1 -0.2
\
FULL 0.4 0.2 120°130 Akihiro OGAWA
4.2 Procedure of Calculation
Eliminating the terms of angular velocity,
linear and angular accelerations from the
2nd and 3rd equations of (4), the following
equations should be solved:
Fy(U, p, 5, Up, bF, UB, 013)=- FE+ Fpv =0
G.(U, /3,5, UF, OF, UBy OB)-= G11+ Gw.---0
FULL LOADI
(12)
First, fixing the ship speed U to a certain value, two curves which satisfy the each of
Eq. (12) is looked for in the range of drift
and rudder angles, p and 5, not more than
+ 300, and from the cross point of the two curves, a necessary combination of p and 3 at the speed can be obtained. The required
lowest speed UL is obtained thus from the
combination of p and 5
as a function of
IBALLAST I (3) 0 BALLAST I
VAIRP4
&reign
440*
(c) (d)Fig. 5 Required Lowest Speed in Wind and Flow
BY
2
UF
Calculations, on the Steered Motion of a Ship under the Action of External Force$ 131
various value of U.
An example of the
procedure is shown in Fig. 4. Of course, for
the successive calculation, it is necessary to
consider in the computor program how to
cope with the case when there are more than
two or no solutions and so on at every
calculating step. By way of example some results of such calculation are presented in
Fig. 5.
The arrows at the center of the
figures denote the direction of ship's course.
lithe lowest speed or the relative speed to
water at the lowest speed were less than
2 knots, as it did not seem to fit
in the
reality, 2 knots or absolute speed
corres-ponding to 2 knots of relative speed was
adopted as the required lowest speed.
4.3 Course stability
The above
obtained solution indicatesMerely a ballanced condition and not the
course stability. Here it is assumed that the
stability can
be judged by
a linearizeddynamic stability without considering the
variation of ux as the first approximation.
Putting the right side of the 2nd and 3rd
equations of (8) as P. and G and equating as:::
aP aP aP'
fo-au, - ar 110! IFLOW DIRECTION , ABC FLOW DIRECTION aC aGaG I
,.gr
, go au, alsthe stability equation becomes as'
d41,
f.40
dzir
(it,gdiso+griir+goily5
Roots, of. the characteristic equation of Eq.,
(14):
+a(72'+,ba+c=0'
where,
a=
)b= fug, frgugo
,e= ugo fog..
indicate the stability indices. The calchla-tions were carried out by a Cardano's method
simultaneously with the calculation of UL.
Some examples of the solution are shown in, Fig, 6. In order to observe the effect of the
difference of speed, roots at double the lowest
speed are also shown in Figs. 6 (a) and (b).. Here an attention should be paid that the roots of Eq. (15) are obtained in connection with Jo, and as the result, there exists very
often a root nearly equal to 0 as is seen in
Figs. 6 (a) and (b). Since the zero-root is out
Fig.. 6 Stability Indices Effected by Wind and Flow
°Or WINO DIRECTION, Ws, = In ,I-4l/17-1. FULL LOAD I U, 2 an at In =....
H.
UL IlPRO011 n calm, ,j.al 2UL I I BALLAST CONDITION U00 km LW =2.1m, (A)_______J.R/-.In calm sea
at 20, \at UL / I I lIBALLASI CONDITION, U, 'DOT Iis.20 W ,,---,U, -...-__ci,,, cairn a IL, sea (a) (b)' (c), (d) 0 + dt
fu+
(15)/'
132 Akihiro OGAWA
of question when, as in general, so far as
only Juy and Jr are concerned, the stability can be judged by the other two roots in this
case. The fact is clearly compared with the case in calm sea, where JO term is not needed.
Though there are many ways to express
the stability,
it seems better
to present directly the characteristic roots in case of the numerical calculation on an electronic corn-putor. If necessary, a solution for a definiteinitial condition can be easily calculated, or
even if the root was not decided, the motion
after a given initial condition can be
calcu-lated without any difficulty',.
repeatedly computing the Eqs. (8) to (11) at
each very small time interval. Though the
time interval can be defined by a
non-dimen-sional method, here it was given by the unit of second for certain reasons.
In case of
this calculation on the mammoth tanker, 1
or 2 seconds were suitable and 5 seconds
gave some difference to the calculated locus.
The following calculations were carried out
at each
1 second intervals. Besides, thesteering velocity was taken as 35°/15 sec. 5.2 In calm sea
First, calculations were carried out in case
of calm sea, where no wind nor flow were
considered. As a matter of course, forces
caused by the relative wind were taken into the calculation even in this case. In Fig. 7
a calculated turning locus at 15° starboard is shown with the corresponding one of a model
test. Since the calculated locus stayes on the same circle also after the last point, the
accuracy of the calculation can be considered
to be enough. The manoeuvring
characte-ristics obtained by such calculation are shown
in Fig. 8. The test results in Figs. 7 and 8
are derived from the free-running model tests
on a 4.5m model by Mori and others"' and
-40° ...30° -20° --- .. -° + .2 .5 6 9 1.0
Fig. 7 Calculated and Tested Turning Loci in Calm Sea 10 20° 30 40° ( STARBOARD ) .3 TEST CALC. TURNING RATE A - - MAXIMUM ADVANCE + SPEED REDUCTION PIVOTING POINT DRIFT ANGLE 1.0
FULL LOAD CONDITION .9
L5.290 m
u16 kn .8
V. .7
.6
FREE RUNNING MODEL .4.5 rn RESTRAIND MODEL
for STATIC DERIVATIVES=1.5 m for ACC. [JERI VAT I VES=2.0 m
for RESISTANCE TEST.6.6
.5 .3 a ° .2 6 ( PORT ) .1
5. Calculation of Turning Motion CALCULATION
30 min
min
=290 rn
5.1 Time Interval of Calculation, etc. ( Fn..0.145)1 5 kn FULL LOAD CONDITION
UF 0 or
The steered motion
of a ship can be
MODEL TE ST1_,4 .5 m =0 kn
calculated by the method described in 2.4, Fn.r.0.16 6
Fig. 8 Calculated and Tested Turning
Characteristics
ACTUAL SHIP TEST .a
z2
)
Calculations on the Steered Motion of a Ship under the Action of External Forces 133
from actual ship test resultsla).
5.3 In Wind and Flow
Calculated examples of the turning loci in
wind, in
flow and in wind and flow are
shown in Figs. 9, 10 and 11 respectively. In Fig. 12, Calculated behaviours of speed, angular velocity, drift angle etc. in calm sea
and in wind and flow are shown.
6. Discussions on the results 6.1 On the method of calculation
The form of derivatives for FH and Gg only
was applied considering the accuracy of the
experiments and the capacity of the computor.
If hereafter the data at the small angular
velocities anddrift angles are
obtained,higher accuracy of the calculation can be
expected in the vicinity
of the
straightFig. 9 Calculated Turning Loci in Uniform Wind
Fig. 10 Calculated Turning Loci in Uniform Flow
1 min U0 /3.
1 5 kn O. 5° -1 .7°
- - 10 1.0°
134 Akihiro OGAWA
course, taking the data into account
in the
form of the intermittent functions of
r, p, and 3.Though this method of calculation is in the
first step of developing the program and it is needed to calculate with various casesfor
instance on a small
boat or at
different (a)BALLAST
U[3,-40 kn
Vti=99,e,
(b)
Fig. 11 Calculated Turning Loci in Wind and Flow
2
Yo/L
manoeuvres, estimating the calculation of
this time, it can be said that the method is
effective as a means of the calculation of the
steered motion of a ship especially in the
point that the external forces can be freely taken in, even when they are not uniform.
A difficult point is that many data are
re-6=35°P -3 -2 0 5 3 -J UF min>1 15 50° -2.2 --2
10
Calculations on the Steered Motion of a Ship under the Action of External Forces 135
2
3 4 5
TIME, t (min)
Fig. 12 Calculated Behaviour of Ship after
Execution
quired for the calculation on a ship, even
with one condition.
Since the theories are
not sufficient to afford such data in good
accuracies at present, massive experiment is needed. For instance, though the forces in x-direction were decided by a very simple assumption in this paper, in order to realize
the calculation, many important factors such
as the effect of drift angle and angular
velocity upon the
ship resistance, wakedistribution and so on, characteristics of the
main engine and propeller and mutual inter-ferences between such factors including the
rudder must be known.
However, the method of calculation itself is favorable in the point that if such condi-tions were fulfilled, since it is very easy to take them into account, a higher accuracy
too°
100°
200°
00°
can be expected and, moreover, the problem of the model-ship correlation could be solved
at the same time. In such sense, it seems
to be favorable to have more concern on the
researches on such method.
The similar approach will be effective and expected tobe applied also to the phenomena of broach-ing, capsize and so son.
6.2 On the calculated results
As the combinations of the external
condi-tions are infinite and the shown figures are
only a few of them, there are many facts
which are not shown. So the considerations
on the calculated results include them.
6.2.1
On the
lowest speed in the straightcourse (Fig. 5)
When the effect of wind is small (In
full load condition as well as in
ballastcondition at low wind speed), the ship tends
almost toward the relative flow direction,
and the lowest speed is limited mainly by
the drift angle except when OF nearly equals to 00 or 180°, and the lowest speed is bigger
when the relative flow directs accrossways. When there is no flow, the effect of
wind appears nearly proportionally to the
wind speed. In full load condition Ur, is
decided by the limit rudder angle, and in
ballast condition, more part is restricted by
the
drift angle and the necessary lowest
speed is bigger.
It shows very complicated effect when there is wind and flow and it seems that there is no general rule in this case. Especially in ballast condition both effects of wind and flow appear almost equally in many cases, imply-ing the difficulty of the manoeuvrimply-ing.
6.2.2 On the course stability in the straight
course (Fig. 6)
Since the stability is here calculated on the above-described minimum speed,
the
ten-dency of the curves to the wind looks some-what different from usual ones. However if
the condition is taken as UB/U constant as
is
used in
general,the tendency of the
stability curves agrees very well to 2) or 3).
(a) When there is no wind, the effect of
flow speed is very small.
2 3 4 T I ME 5 t (min) 10 9 4 -3 9 7 5 6 II 2 = =180° UB =40 FULL LOAD =15 kn
When there is wind only, the stability
varies with wind direction, is less than that
in calm sea and is unstable for the wind
from the stern. The change of the stability index according to the variation of the wind
speed is similar to the effect of the flow
speed. In some conditions, the stability be-comes periodic.When there is wind and flow, the same description as 6.2.1 (c) will do. However in
the stable range in calm sea in full load
condition, for instance, the stability hardly varies for the wind from every direction.
Though it seems meaningless to decide
the lowest speed in the unstable range, it
will still be of use since it is considered that
the ship can change course to an arbitrary
direction by steering from this state (for that
purpose the limit rudder angle was chosen smaller), and that even an unstable ship can keep her course by a suitable manoeuvring.
The course stability indicies are decided by UFIU and UBIU, and the smaller are those
ratios, the nearer to the value in calm sea
become the indicies. The unstable range in
Fig. 6 is caused by the big value of the above ratios.
6.2.3 On the turning in calm sea (Figs. 7 and
8)
(a)
In Fig. 8 the calculated r'd at small
rudder angles appears more stable than that of the tests. The reason is that the
hydro-dynamic forces are expressed in the form of third-order derivatives and the characteristics
of the ship in such condition is not
repre-sented perfectly.
(1)) The difference between calculation and
test in the range of big turning rate seems
to be caused by the imperfect estimation of
E. The improvement of this point will be
an important subject in the following step.
(c)
The reason of the difference of the
speed drops is that the calculation is based
on the assumption of constant power, and on
the contrary the model test
is carried out
on the basis of constant propeller revolution using D.C. shunt motor. This also seems to
be a reason of the shift of the position of
the turning circle in Fig. 7.
(d)
The turning
becomes steady afterabout 2700 turn regardless of the approach
speed.
6.2.4 On the turning in wind and flow (Figs. 9-12)
(a) The average direction of the
macro-scopic " drift " of the steadily turning ship
does not necessarily coincide with that of the
uniform wind or flow.
And the average
speed of the " drift " is smaller than that of
wind.
(b)
These effects vary with the loading
condition, ship speeds, speed of wind and flow
and so on.
In general the effect of the
external condition is bigger at lower speed,
and the effect of wind is bigger in ballast con-dition and that of flow in full load concon-dition.
(c) The linear and angular velocities and
the other items of ship vary periodically
during the turning, though the forms of the variation are not simple.
7. Conclusions
The following conclusions were obtained
concerning the method of the calculation and the calculated results on the steered motions
of a ship in wind and flow.
( 1 ) The non-linear equations of the
un-steady motion of a ship can be calculated
numerically on a digital computor.
( 2 ) The required minimum speed and the
course stability in a straight course within
the limits of definite rudder and drift angles
can be calculated.
( 3 )
In some cases the course stability
index has a periodic solution.( 4 )
At the above-mentioned minimum
speed, the ship tends to be course-unstable
mainly in case of following wind, though the stability is
improved by the higher ship
speed.( 5 ) The effect of wind and flow change remarkably according to the loading condition of ship.
( 6 ) The average direction of the macro-scopic " drift " of the steadily turning ship
does not necessarily coincide with that of the
CalcuTations on the, Steered Motion of a Ship under the Action of External Forces 137
uniform wind or flow, and the average speed
of the "drift" is smaller than that of wind.,
8. Acknowledgement
The author expresses. his gratitude to Dr.
Y. Yamanouchi, Vice Director, Ship Research
Institute and Dr.. T. Hanaoka, Head, Ship
Dynamics Division for their continuous
guidance on this work, to Messrs N. Mori, T. Tsuji and M. Kan for their great deal of
experiments, to. Mr. K. Nonaka for his
corn-putor programming on the derivatives, to
Messrs. T. Yamamoto, T.. Saruta and T..
Sato for their collaboration to the experiments
and to members of committee II of JTTC
, and the members of Ship Dynamics Division for their timely discussions on this research.
The calculations, were carried out on a
digital computor FACOM 270-20 at ShipDynamics Division programmed in
FOR-TRAN. The author is also indebted to Mr.
S. Ando of the Division for his frequent
discussion on the
programming and theappliCation of the computor, since majority
of the research times were spent for the
development of the computor programs-.
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