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Laboratorium voor Schaepc.hydrornechanica Archief Mekafweg 2, 2528 CD Deift Tel.: 015- 783373 - Fax:015- 781035 Z50545 - Pubi. MARINTEC DRIFT FORCES IN DIRECTIONAL SEAS by: J.A. PinksterPaper to be presented at: MARINTEC CHINA '85
Shanghai, December 2-8, 1985.
-1--DRIFT FORCES IN DIRECTIONAL SEAS
by: J.A. Pinkster
Head Project Department/Ocean Engineering Division Netherlands Ship Model Basin
The Ede/Wageningen Laboratories of
1. INTRODUCTION
The analysis of the behaviour of vessels moored at sea
is generally based on measurements from
model tests in
ir-regular uni-directional waves carried out in
suitable model facilities.
Data obtained from such model tests has in the past
proved to be indispensable in the design of
offshore
float-ing structures. Although, at all times, the
conditions of
the model tests represent a simplified reality, the
on-site
performance of full scale structures bears witness
to the
general validity of such model test data as a sound basis
for judging the performance of
a particular design with
regard to both the motion behaviour and the loads
on the structures.
Notwithstanding, however, the generally accepted
valid-ity of model testing under such simplified conditions, there
is a need to investigate, in more detail,
the effect of
directional spreading of irregular waves, as
it occurs in reality, on the loads and motions of floating offshore
structures. See, for instance, ref. [i].
One method of obtaining such information is to conduct
model tests in basins fitted with wave
generators which have
the capability to generate irregular directional waves. Such
model tests will produce quantitative data, based ori a
phys-ical reality, of the effects of directional waves. [i], [2
-3-Another method of obtaining data
on the effects of
multi-directional seas on the behaviour
of floating
struc-tures is based on
theoretical computations; [4]. It will be
clear that efforts
should be made to compare results of such
computations with model test results. This
is necessary
since significant physical effects
peculiar to directional
seas may be present which are not accounted for in
the theo-retical approach.
For irregular uni-directional seas,
computer programs
exist which can, with reasonable
accuracy, predict the
be-haviour of a moored vessel in both the
frequency and the time domain; [5] and [6].
This type of computer program can be used
to assess
certain aspects associated with multi-directional seas
pro-vided a realistic formulation
can be given for the
waveloads, both oscillatory, first order wave loads
and mean and
low frequency second order drift forces in irregular
direc-tional waves, [7].
In this study attention is paid to such formulations
for the mean and slowly varying drift forces.
Expressions
are given for the wave drift forces for the case that the
undisturbed incident directional wave field is described by
a Fourier series with random phase angles.
Based on such descriptions for the second order wave
loads, frequency domain results
are obtained in terms of
expressions further insight can be obtained regarding the
effects of directional seas.
Attention is also paid to representation of second
order wave loads using the Volterra series or Functional
Polynomial approach. This allows the use of measured random
irregular time records of waves approaching the body from
various directions combined with second order impulse
re-sponse functions in order to generate force records in
multi-directionál waves for the purpose of time domain
simulations.
Numerical results on the wave drift forces in a special
type of directional sea, namely, regular cross waves,
ob-tained using three-dimensional diffraction calculations and
direct integration of second order pressure are compared
with results of model tests.
Results are also given of tests in irregular
uni-direc-tional waves and of tests in irregular cross seas on the
basis of which the validity of the superposition principle
with respect to mean drift forces could be checked. For
b-
-5-2. THE INCIDENT WAVES 2.1. General
In order to derive expressions for the drift forces in
directional seas we will first choose an appropriate
de-scription of the irregular directionally spread sea. We
assume that the wave elevation in a point can be described
by a double Fourier series, which characterizes the surface
elevation as a sum of regular long-crested waves from
vari-aus directions: N M (t) = E E . cos(w.t + e. i
ik
i=l k=l (2.1) in which: = wave frequency = random phase angleN = number of discrete frequency components
M = number of directional components
= wave amplitude
i = wave frequency index
k = wave direction index.
In a multi-direction sea the amplitudes of the wave
components are found from:
= /2 s (w.»4. ) J L)
ç i (
where:
S(wi,1Pk) = directional wave spectrum = frequency interval
= direction interval.
For the directional spectrum various
formula-tions can be chosen, [8] and [9].
After chosing the random phase angles, a time record of
the surface elevation can be computed from equation (2.1).
2.2. Evaluation of wave elevation in time
The computation time necessary to evaluate the double
summation can be reduced by replacing equation (2.1) by the
following equivalent expression:
N
(t) E (a. cos w.t + B. sin .t)
i J_ i i 1=1 in which: M a. = E . COS E.
k1
M B. = - E . Sin E. k=l ikik
(2 3) (2 4) (2 5)This shows that by first computing the coefficients ai
and B1 the wave elevation at each time step can be found
average:
S(w.) w = (. cos w.t + . sin
i i i i
2.3. The spectrum of the wave elevation measured in a ncint
Having selected this description for the waves it is of interest to check the properties of such a discrete formula-tion. For this we chose the wave spectrum.
The point spectrum S(w) can be
found from equation(2.3) by taking the mean square, or variance, of the wave
elevation component with freauency w as follows:
(2.6)
where the overbar indicates that the mean value should be
taken.
Given a particular realization of (t), i.e. a fixed
set of phase angles £.k, equation (2.6) results in:
which, taking into account equations (2.4) and (2.5),
re-suits in:
M M
S(w.) = ½ z z cos(c.k - . . . . (2.8)
i
k1 £=l
This shows that the spectral density of a particular reali-zation is a function of the random phase angles E.k and
Averaging equation (2.8) over all realizations (all
possible Lik and values) gives the following ensemble
M
2
E{S(w.)
SCi)] = ½ Eik
i
k1
This result implies that with respect to the spectral density the wave elevation formulation given by equation
(2.1) is non-ergodic, i.e. time averages are not equal to ensemble averages. A consequence of the non-ergodicity of
such formulations is, for instance, that the wave spectral
density, for any particular realization, becomes dependent on the location in the horizontal plane; [lo].
Ta}ing into account equation (2.2), equation (2.9)
becomes:
M
E[S(u.)
w] =
E Si'k
i
k1
Eliminating Lw on both sides and passing from a discrete to a continuous formulation results in:
27r =
f
d= S(w.)
i
o(2 9)
(2 10)
(2.11)
which shows that the point spectral density of a realization
of the type given by equation (2.1) is only equal to the
input point spectrum in the ensemble average sense. A more detailed analysis of the properties of the double Fourier
series description in which also the phenomenon of wave
grouping, which is of importance for the low freauency drift forces, is t&ken into account, has been given in [li] and [12].
-9-3. SECOND ORDER WTE DRIFT FORCES 3.1. General
Second order wave forces acting on vessels or
struc-tures in waves can be computed based on direct integration
of second order pressures and forces, [13]
In vector notation the general expression for the sec-ond order wave forces is as follows:
(1)2 = - f ½pg n dl - 5f {- ½ V (1) 2 -
ndS+
r WL S o - 5f {_((1) v('))}
dS + X ( (1)) ± t g S o - If {- + dS s o (3 1) in which: 1)= first order relative wave elevation around the water-line WL
(l) = first order velocity potential including effects of
incoming waves, diffracted waves and waves generated by the body motions
mass matrix of the body in vacuum
first order oscillatory linear motlon vector
first order oscillatory angular motion vector of the body
outward pointing normal vector to the hull mean wetted hull surface
M =
(1)
X = = = S0 =(2)
= second order "incoming wave2' potential
(2)
second order "diffraction" potential.
3.2. Realizations of drift force records in time domáin
Equation (3.1) shows that the second order force
con-sists of terms involving products of first order quntities or integrals of products of first order quantities.
Using the discrete formulation of equation (2.1) for
the waves it follows that the second order force in irreg-ular directional seas can be written as:
N N M M
F2(t)
= E E E ç. P. cos{(w- wjt +
jik
i Ji=l j=l
:k=l £=l+ (E.
-ik)}+
N N M M + E E E E ik sin (. - (Ü .)t +i J i=1 j=l k1 £=lin which Pjj and are the in-phase and quadrature
quadratic transfer functions derivable based on equation
(3.1).
For instance, for the quadratic transfer function due
to the first contribution for equation (3.1) we may write, in vector notation:
-11-pijki
= -
f
/4Y
Y
cos(E
- E
) (3.r. r. r. r.
WL 1k j9. lic ji
0ijki =
f
1/4PgY
Y
Sin(E - Er. ) dl . . (3.4)WL ik ji 1k ji
in which:
= first order transfer function for the relative wave
r. ik
elevation for wave frequency w and wave direction
Er = phase angle of relative wave elevation
j.k
= direction cosine of the waterline element dl with
components n1, fl2, n3
i, j = wave frequency indices
k, £ = wave direction indices.
Each of the components of equation (3.1) contribute to
the total in-phase and quadrature quadratic transfer
func-tions. This will not be treated further here. It should be
mentioned that evaluation of these transfer functions can be
made through the application of 3-D diffraction computer
programs, [13].
The contribution due to the non-linear potentials (2)
and (2) are approximated using the method given in [13]
making use of the non-linear second order potential for the
undisturbed directional waves given in [14] . For irregular
long-crested waves the validity of this approach was
recent-ly demonstrated by comparison of results obtained using this
approximation and results based on a more exact solution
We will assume hereafter that the quadratic transfer
functions include contributions from all components of
equa-tion (3.1). It should be noted that through regrouping of
terms such as given in equations (3.3)
and (L4) certain
syrrinietry relationships will apply to Pjj and These will be given in a later section.
3.3. Mean value of realizations of wave drift force records
The time average drift force is found from equation
(3.21 for 1j: (2) N M M F (t) = Z
f
1ikL cos(E.- c.) +
i=1 k=l 2. 1 + 0iikZ sin(s. - c. ) -11ç -i2.It can be shown that the ensemble average of the drift
force is:
N M
E[F2]
= = E E 2 pj=1 k1
k iikkwhich, in continuous form becomes:
2ir = 2
f
f
S(u,ct) P(w,w,,)
d dw00
(3 5) (3 6) (3 7)in which P(w,w,c,cz) is the quadratic transfer function of
the mean drift force in regular waves of frequency w from
-13-3.4. Frepuency domain representation of the drift forces:
Drift force spectrum
It is of interest to obtain information on the low
fre-quency drift forces in irregular waves in the frefre-quency
do-main. To this end we use equation (3.2) as starting point to
obtain the spectral density of the drift forces.
The derivation of the spectral density will not be giv-en here. The procedure is similar to that followed in Sec-tion 2.3 for the wave spectrum. As is the case with the wave
elevation in a point as given by equation (2.1) the second
order force given by equation (3.2) is non-ergodic and for a
particular realization (choice of s) the spectral density
of the force is dependent on the phase angles c.
The average over all realizations (ensemble average) is found to be: 21T 2i
sF() = 8
f
Jf
s (+p,a) d d dw000
(3 8) in which:T(±p,w,,$) =p(+,w,cr.,) + iQ(w+i,w,a,)
For the quadratic transfer functions the following sym-metry relationships apply:
p(w--,,,S)=
p(ui,w+7a
(3.9)
(311)
which is the same as:
T(w+p,w,a,)=T*(,w+i,,a)
(312)in which * denotes the complex conjugate.
Similar symmetry
equations apply to the discrete quadratic transfer functions
ijk 0ijk and the amplitude TjjkL.
3.5. Drift forces in irreqular cross seas
We will apply equation (3.8) to a simple case to show
the effect of wave directionality on the wave drift force.
To this end
we assume that the irregulardirectional sea
consists of a superposition of two irregular long-crested
uni-directional seas approaching from directions and a1
respectively. This type of sea condition is known as a
cross-sea condition.
The
relevance of the effect ofsuch sea conditions on the behaviour of moored vessels has been dem-onstrated in [i].
The directional wave spectrum of irregular long-crested waves from the direction a0 is defined as follows:
S (w,a) = (a-a0) S (w) (3.13)
a0 a0
in which the DIRkC delta function is defined
-15-The directional wave spectrum of two long-crested
ir-regular waves from directions a0 and a1 is:
S(w,a)
= S(a-a0) S (w) + 6(a-a1) S (w) . . . (3.16)a0 ai
in which S (w) and S (w) are ordinary point spectra for
a0
long-crested waves.
The mean drift force in an irregular directional sea is as follows:
2ir
= 2
f
f
S (w,a) P(w,w,a,a) da dw00
Substitution of equation (3.16) and taking into account
equations (3.14) and (3.15) gives:
F F
+F
a0 a1 = 2f
S (w) P(w,w,a0,a0) dw + O a0 + 2f
S (w) P(w,w,a1,a1) dw o cil (3 17) (3 18) L = 0 for ci a0 (3 1 and: 2f
-)
da = i (3 5) oThis sl-iows that the mean drift force of two sea states is
the sum of the mean forces from the individual wave trains.
The spectrum of the wave drift force in an irregular
sea is: 2ir 2iî = 8
f
f
f
S(w+p,a) S(w,)jT(w+,w,a,)I2
000
(3 19) Substitution of (3.16) gives: 2î 2irSF()
= 8f
J
f
{(a-a0) S (w+.i)+ 6(a-a1)
So o o a1
{6(-a0) S (w) ± 6(-a1) S (w)]
a0
which results in:
SF()
= 8 J S (w±u) S (w) T(w+,w,a01a0)j2 dw + O aOa0
+ 8 J s(w) S
()
1T(w+,w,a0,a1)I2
dw + O a0 a1 + 8 J S(w+) S
(w) T(w+,w,a11a0)l2 dw + O a1 + 8J
S (w+) S (w) !T(w+,w,a11a1)2 dw O a1 a1 (3 21) da dS dw (3 20)
-17-The first and last terms of equation (3.21)
correspond
respectively with the drift force
spectrum from each of the
two sea conditions
separately. This shows that the low
fre-quency second order excitation in
a sea state consisting of
two long-crested irregular seas is
larger than the sum of
the excitation from each sea
independently. The second and
third terms of equation (3.21)
show the excitation arising
from interaction of both long-crested
seas. The nature of
these terms also shows under which
conditions such inter-action terms may be neglected.
Consider, for instance, that waves from
direction a0
are relatively short, wind driven seas while those from
di-rection a1 are relatively long-period
swells. oth spectra are shown in Figure 1.
If the spectra have little or
no overlap on the
fre-quency axis, then the products of the spectral
densities in
the second and third parts of equation (3.21)
are small,
even for relatively large p values. This
can have important
consequences for simulation computations since such
combina-tions of wind driven and swell seas
frequently occur. The
impact of this effect will be apparent when
it is realized
that the major part of the low frequency response of moored
vessels is at or near the natural frequency.
These
frequen-cies are generally very low. The consequence of this effect
is that the system only reacts to very low frequency
compo-nents in the excitation. If the above-mentioned
separation is present then equation (3.21) shows that the
excitation may be assumed to be simply the sum of the
exci-tation arising from each sea independently.
For the case that both long-crested irregular wave
trains are from the same direction , equation (3.21)
becomes:
= 8 J {s
(+i.,a)
(w,)
+ S (w+.i,a)s
(w,a)
+o
+S(ui+j,a) S
(u,)+S (w+p,)
s(w1a)]
which, with =
= , is the same as:
sF() = 8
Js
(w+M,a) S (w,a)T(w+p,,a,a)[2 dw . . (3.23)o
in which:
S(w,a) = S
(w,a) + S (w,a) (3 24)a1
Equation (3.23) is again the well known result for
uni-directional waves.
The aforegoing discussion shows that combinations of
uni-directional seas interact in such a way that the
resul-tant oscillatory part of the drift forces is always larger
-19-than the sum of the drift forces arising from each wave
train independently.
The constant (mean) part of the drift forces as given
by eauation (3.18) does not suffer the same interaction
effects.
The mean force in
two uni-directional irregularwave trains from directions and is simply:
= 2 5 S (w) P(w,w,a0,a0) dw +
O a0
+ 2 5 s (w) P(w,w,a1,ci1) dw
O a1
(3 25)
This shows that the mean is equal to the sum of the contri-butions from each wave train independently.
Equation (3.25) is, however, only true in the ensemble
average sense. Time average values of particular
realiza-tions as given by equation (3.5) retain interaction terms due to the fixed choice of the phase angles. The influence of these interaction terms on the time average values re-duces as the number of frequency components is increased,
4. APPLICATION OF THE FUNCTIONAL POLYNOMIAL OR VOLTERRA SERIES TO FIRST AND SECOND ORDER WAVE LOADS IN IRREGULAR DIRECTIONAL SEAS
4.1. General
Within potential theory it is assumed that the
poten-tial describing the flow and all quantities derived from the
potential may be expanded in a convergent power series. For instance, for the wave force:
F =
F(0)
+ EF1
+£2F(2)
±. o
(4.1)
in which:
(0)
F hydrostatic force
F1
= first order oscillatory wave loadsF2
second order wav loads, the low frequency part ofwhich is known as the drift force
C = a small parameter (wave steepness).
In such cases the Volterra series expansion is also
valid, [16] and [17]: + F =
F°
+f
(t-r)
h(1)(T) dt +±
+f
f
ç(tt1) (tT2) h(2)(11T2) dt1 dt2+ +(4.2)
in which:
(t) = wave elevation record
T, T1, '2 = time shifts
h(1)(T) = first order impulse response function = second order impulse response function.
4.2. Wave field
We consider the wave field to consist of a
superposi-tion of long-crested irregular wave trains from discrete
wave directions. in which: N -i(w.t + . = Re { e ik i=l
We furthermore suppose that the wave elevations k = 1 . .. M are available as time records.
4.3. Mean and low frequency second order wave drift forces We may rewrite equation (3.2), which gives the low
fre-quency drift force in irregular directional seas, as
fol-lows: M M
F2(t) =
Z Z Re tF(2)(t)] Lk1 £1
-21--(4 4) (4 5) M (t) = (4 3)in which: N N -i{ (w. - w .)t
± (E.
- E.
) }F(t) = E
E T.jkz ek
-1=1 j=l (4 6)The equivalent Volterra series expression for equation (4.6)
is as follows:
F(t)
=f
f
k(t_Tl) (t-T2) h2kL
(T1T2)
dT1 dT2- ...
(4 7)
Equation (4.7) will be set equal to equation (4.6) in
order to determine the form of h(T1T2).
To this end wewrite for the wave elevations k(t_Tl), (t-T2):
N -i(w.t
+ E.
) jw«r i ik i Re [ Z e - e . . (4.8) ik i=l N-i(w.t ±
i
i
. )jw.T
i
2,Re [E
e e j . (4.9)Products of wave frequency quantities contain both sum
and difference frequencies which are found from:
k(tTltT2)
½Re[k(t_rl)(t_r2) +(t-T1)(t-T2)]
-23-where the *
denotes the complex conjugate. The (complex)
wave levations in the right-hand side of
equation (4.10) are given by the expression inside the [
j in equation (4.8)
and equation (4.9).
Substitution in equation (4.7), neglecting sum
fre-quency components, yields:
+ +
N N -±{w.- w.)t + (E - E )lF(t)
f
f
½Re[ E E e i ik -j9.-=
1=1 ik jLj(w.T
i i- W.T
j 2
j h(i1i2) di1 dT2
. . (4.li)e
In order to determine h(i1i2)
we will equate
thecoefficients of cos {(w1
- w)t +
-ik
- E.)} and of sin
{(w1
- w)t +
- in equation (4.6) and equation
(4.11). This leads to the following expression:
-- -- i(w.i - W.T ) Tjjk
= ½ f
f
h(T1i2)
1 1 j 2 di1 dt2 e (4.12)from which it follows that:
+ +
-i(.i
- w.t )e
f Tijk 1 1 2 du. dw.
--
i Jwe will use equation (4.13) to determine a symmetry
rela-(2)
tionship for h (T1T2).
According to equation (3.12):
This results in the following symmetry relationship for
(2)
tLL (T1T2):
(2)*
_hjk
(t2T1)We now return to equation (4.5) and reformulate this as
follows: M M
P2()
= E E½Re[F(t) + F(t)]
. . . (4.16)k1 £=1
with: for = 2 for k L (4 17)Taking into account equation (4.7) and the symmetry re-lationship of equation (4.15) we find:
(4 15)
F2(t)
= M M±+
(2) = E E ½Re{f
f
k(t_Tl (tt2) hkj (t1t2) dt1 dt2 + + L (t_Tl)k(t_T2) h (t1t2) dt1 dT2] . . (4.18)Interchanging
t1
and T2 in the last part leadsto:M M
+±
F2(t)
E E ff
ck(t_rl) (t-t2) k=Z £=1 (2)*½ {(t1t2) + h
(t1t2)] dt1 dT2 M M++
= E Ef
f
k(t_T1) C2(t--r2) k=2. £=1- -25-Re
[h2()J
dt1 dT2 ic,. (4.19)The real part of h(T1t2) is found from equation (4.13).
4.4. Discussion
In equation (4.19) use can be made of arbitrary random records k(t) and (t). These may be generated, for instance, based on filtered time records of white noise for which the filters are chosen to suit the required
direction-al spectrum shape as a function of directional index k.
Alternately, for the case of cross seas generated in model
corn-ponents, which can be generated and measured separately, can be used.
This presents the possibility of comparing time records
of computed and measured wave drift forces on a vessel in
long-crested irregular waves from two directions. Tests of
this kind will reveal the basic effects of the influene of
directional spreading of waves, while retaining the
require-ment that the wave field should be well defined. At this
time this is still a problem with respect to directional
seas generated in model basins using large numbers of wave
5. SOME AS PECT S OF THE RELATIONSHI P BETWEEN WAVE FORCES IN UNI-Dl RECT 10MAL AND MULTI -DIRECT 10MAL WAVES
5.1. General
In this section the effect of the directional spectrum
S(w,) on the mean and spectral density of the low
frequen-cy drift force is briefly discussed.
Two formulations for the directional spectrum are in
general use. The simplest of these is:
-27-in which:
= frequency dependent point spectral density
f()
= a spreading function.For the point spectral density any of the current
spec-tral forms, i.e. JONSWAP, Pierson-Moskowitz, etc., may be
chosen. For the spreading function, a function which is
pos-itive and symmetrical about the dominant wave direction is
generally chosen, [8] and []
The spreading function has to be chosen in compliance
with the following equation:
2i 27r
S ()
=f
S (w,a) da =f
S () f(a) da . . . .(5.2)
o o
or:
2ir
f
f(a) da = 1 (5 3)o
A slightly more complicated formulation is as follows:
S(w) f(w,)
which yields the following condition:
2Tr
J f(w,a) da = i
0
(5 4)
(5 5)
In this case the spreading function varies with the wave
frequency w. Equation (5.4) allows directional spectra with,
for instance, different dominant wave directions depending
on the wave frequency and also different degrees of direc-tional spreading dependent on the wave frequency.
In order to give an impression of the effect of
direc-tional spreading on second order drift forces use will be
made of equation (5.1).
5.2. Mean and low freouency drift forces
The mean second order wave drift forces in irregular
directional seas are obtained from:
2ir
= 2
f
f
S (w,a) P(w,w,cx,a) da dwApplication of equation (5.2) gives:
2ir
= 2
f
S(w) {f
f(a) P(w,w,cz,a) da} dw. . . (5.7) o o = 2
f
S(w) P(w) dw o in which: 2iîP(w)
=f
f(a) P(w,w,a,a) da oThis shows that P(w) can be interpreted as a weighted mean
drift force coefficient.
Another way of presenting equation (5.7) is as follows:
2rr
F =
f
f(a) F(a) dOE oin which:
2
f
S (w) P(w,w,a,a) dwo
-29-where F(a) is the mean drift force in uni-directional seas
from direction OE for the spectrum s(w).
The spectrum of the low frequency drift force follows
from:
(5 8)
(5 9)
(5 10)
2iî 2ir
= 8
f
f
f
Sd dw
000
(5 12)
which, using equation (5.2) becomes:
2î 2u
sF(P) = 8f
S(w+) S(w){ f
f
f(a) f(s) 000
T(w+p,w,,)l2dd}dw
(5.13) = 8f
s
(w+j) S (w) F(w+p,w) dw . . (5.14) 0 in which: 21T 2iTF(w+,w)
= Jf
f(a) f(s) 1T(w+,w,a,)j2 d d00
(5 15) 5.3. ConclusionsIn this section some aspects regarding the relationship
between forces in uni-directional and
multi-directional
waves have been briefly highlighted. The results obtained
using the simplest formulation for the directional
spectrum
show that uni-directional data can, in many cases, be easily
-31-6. MODEL TESTS 6.1. General
In the previous sections a general outline of the
the-ory regarding mean and low frequency second order wave drift
forces has been given. It was found that, given a
descrip-tion of the irregular direcdescrip-tional wave field in terms of
either a set of spectra of long-crested irregular waves from
dis crete directions or a continuous directional wave
spec-trum, the second order drift forces can be determined if the
frequency and wave direction dependent quadratic transfer
functions
ijk and are known.
-It was indicated in Section 3 that these could be
ob-tained based on 3-D diffraction calculations. In this
sec-tion results of such calculations will be compared with
results of model tests for some simple, fundamental cases.
The model tests and calculations have been carried out
for a 200,000 DWT fully loaded tanker moored in a water
depth of 30.24 ni. The main particulars of the vessel are
given in Table 1. A body plan is shown in Figure 2.
The model tests were carried out at a scale of 1:82.5
in the Wave and Current Laboratory of the Netherlands Ship
Model Basin. This facility measures 60
m by 40
ni with avariable water depth up to 1 m. The basin is equipped with snake-type wave generators on two sides of the basin. The
wave generators on each side can be driven independently to produce regular and irregular cross-sea conditions.
Model tests were carried out in regular cross-wave
con-ditions and irregular uni-directional and cross-sea
condi-tions. In the following a brief description will be given
with respect to the choice of the test conditions, the
re-suits of tests and the comparison with results of
computa-tions.
6.2. Tests in regular cross waves
According to equation (3.5) the mean force in irregular directional seas is given by:
N N M
F(2)(t) = E Z E
j2 {p11 cos(E. - s ) +
ik
i
i=l k1 £=1
Each of the terms in this equation reflects a
contribu-tion due to interaccontribu-tion of a regular wave with frequency Wi
from direction k with a regular wave with frequency W from
direction L.
Consider the case that we have one regular wave with
frequency w1 from direction i and one regular wave with the same frequency from direction 2.
The mean drift force would then be:
F(2)(t) =
2
- 11 P1111 + l2 ll22 + 1l ç12{P1112 cos(511 - 12 +
+ 0kL
sin(s.1k
- C.)'
-33-+ Q1112 sin( - E12)} +
l2 11{p1121 COSCE12 - cil
Taking into account the symmetry relationship of equations
(3.10) through (3.12) this results in:
F2(t)
2 2= 1l llll ± l2 ll22 +
+ 2 C11 C12 {p1112
cos(E11 -
c12) +The first two components of equation (6.3) are the mean
forces due to each regular wave independently. The third
contribution is due to interaction effects of the two
reg-ular waves in the mean drift force. It is seen that this
component is, besides being a function of the quadratic
transfer functions P1112 and
1112' a function of the phase
angles E11 and E12 of the two regular waves.
The quadratic transfer functions P1111 and P1122 can he
found from tests or computations for regular waves from one direction. For this particular tanker, these uni-directional mean drift force transfer functions have been given in [13].
The purpose of the tests in regular cross waves is
spe-cifically to identify the quadratic transfer functions P1l12
) ±
+ Q1121 sin(c12 - (6 2)
and Q1112 which represent the interaction effects due to the
simultaneous presence of two regular waves.
Equation (6.3) shows that, in order to identify these
effects, tests in regular cross waves should be carried out
whereby in each test two regular waves with the same
fre-quency and amplitude are generated. The phase angle
differ-ence of the components (E:11
-
E:12) must be different foreach test however.
From equation (6.3) it is seen that the measured mean
drift forces on the vessel will then contain a mean part and
a part which is a harmonic function of the phase angle dif-ference
(C11 -
C12).We have chosen to carry out tests in regular cross
waves with the component waves at right angles to each other and at 45 degrees to the port and starboard bow of the
ves-sel respectively. The set-up is shown in Figure 3.
Regular waves were adjusted separately from both sides
of the basin. The frequencies were the same and the wave
amplitudes (first harmonic component of the wave elevation
record) measured at the mean position of the centre of
grav-ity of the vessel were almost the same. A review of the
reg-ular waves adjusted from each side of the basin is given in Table 2.
During the tests in regular cross waves, the drive
shafts of the wave generators on both sides of the basin
-35-.
adjustment of the phase angle difference - £12) from
one test to the next and at the same time assuring that both
wave generators were running at the same frequency.
The model of the tanicer was moored in a soft spring
mooring system. The longitudinal and transverse forces
ex-erted by the mooring system on the vessel were measured by
means of force transducers situated at the fore and aft
con-nection points of the mooring system. The set-up is shown in Figure 3.
Series of tests were carried out in regular cross waves
of a given frequency and amplitude whereby the phase angle
difference - £12) between the component regular waves
was changed by 60 degrees for each consecutive test. In each
test the mooring forces were measured. The time average of
the mooring forces yielded the mean longitudinal and
trans-verse drift forces and mean yaw moment as a function of the
phase difference.
The results of measurements are shown in Figures 4
through 7 in terms of the mean forces and yaw moment to a
base of the phase angle between the wave generators. Also
included is the amplitude of the first harmonic of the
re-sultant undisturbed wave elevation measured at the centre of gravity of the vessel.
The results shown in these figures confirm that the
mean forces contain a constant part and a part which varies
periodically with the phase angle difference of the wave
Due to the symmetry of the test set-up,
i.e. regular
waves of the same frequency and approximately the same
am-plitude approaching from 135° and 225°, the mean values of
the transverse force F and the yaw moment
should be
equal to zero leaving only the periodic
component of the
mean force and moment. Due to slight differences in wave
amplitudes and possibly due to slight error in model
align-ment this is not quite the case. The periodic parts of these
mean forces are, however, dominant.
The mean longitudinal force F contains a mean
compo-nent corresponding to the sum of the mean forces due to the
component regular waves and the additional component which
is periodic with the phase difference between the wave
gen-erators.
When comparing the mean forces and yaw moment as a
function of the wave generator phase angle difference, it is
seen that except for tests at wave frequency 0.267 rad/s,
the mean transverse force is in phase with the mean yaw
mo-ment. At 0.267 rad/s, a phase di'fference of about 1800 is
seen between these quantities. In geñeral, the mean
longitu-dinal force F is about 90 out-of-phase with F
and M.
This is in agreement with equation (6.3) when the symmetry
of the test set-up and wave conditions are taken into
ac-count.
In a fully symmetrical case in regular cross waves,
-37-zero, the wave elevation pattern consists of a square
pat-tern of three-dimensional peaks and troughs travelling in a
direction parallel to the longitudinal axis of the vessel
with the maximum peaks and troughs moving in a line exactly on the centre line of the vessel.
In this case the mean transverse force F and ya
mo-ment are equal to zero. Assuming that the component wave
amplitudes are equal, this implies that for the transverse
force and yaw moment, the value of
1112 in equation (6.3)
is equal to zero. Based on similar reasoning it can be shown
that for the mean longitudinal force Fi the value of
is equal to zero.
Consequently, according to equation (6.3) the varying
part of F
will be 900 out-of-phase with respect to thevarying parts of F and M1. The periodic part of the
varia-tions in the mean value of the forces to a base of the wave generator phase difference are governed by the third
compo-nent and fourth compocompo-nent for and for F1 M1J) respectively
in equation (6.3).
In order to compare
the results of model tests inregular cross waves with the results of computations, the
following analysis was applied to the measured data:
From the results given in Figures 4 through 7, the am-plitude of the first harmonic of the mean forces and moment
and their respective phase angles relative to the origin
thus obtained were divided by 2 21 i and
2 being the
amplitudes of the component irregular waves given in Table 2 for the various frequencies.
For the surge force F, the computed values cf the
qua-dratic transfer functions and are given in Table
3 and in Table 4 for the case that the direction index k
corresponds to the waves from 135° and the index £
corre-sponds to waves from 225°.
All combinations have been given. In this paper use is
only made of results for the case ij. The cases when ij correspond to regular cross waves with non-equal
frequen-cies.
For comparison purposes, the quadratic transfer
func-tions for the surge force are also given for the case that
both waves come from the same direction, i.e. for the case
that k is equal to L. These results are given in Tables 5
and 6.
The transfer functions were then compared with the
com-puted values of the amplitude T1112 for F, F and M1,. The
results of the comparisons are shown in Figures 8 through lo.
The phase angles, CFç of the forces and moment
rela-tive to the point at which the amplitude of the undisturbed
regular cross waves is at a maximum are also compared with
-39-In general, the amplitudes of the quadratic transfer
functions T1112 are reasonably well predicted by the
compu-tations as are the phase angles relative to the undisturbed
regular cross waves. On the whole, the agreement is
consid-cred to be satisfactory.
6.3. Tests in irrecular cross seas
In the previous section model tests in regular cross
waves were described. It was seen that, dependent on the
relative phase angles of the component regular waves, mean
drift forces could be higher or lower than the total mean
drift force due to the sum of the drift forces from each
wave component independently.
In irregular seas all relative phase angles between
wave components from different directions are equally prob-able. The result of this is that the total mean drift forces
in irregular seas is simply the sum of contributions from
all wave components. This is
expressed in equation (3.7). forthe general case of directionally spread seas and in
equa-tion (3.18) for the case of irregular cross seas consisting
of a superposition of two long-crested irregular wave
trains.
On the other hand, if we consider that in an irregular directional sea the relative phase angles between wave
com-ponents from different directions are continually changing
reflect the additional low frequency force components due to
interaction effects predicted by, for instance,
equation
(3.21).
Tests in irregular cross seas were carried Out to check
whether the theoretical prediction is borne out by
experi-mental findings with respect to the mean forces.
The model set-up was the same as used for tests in
regular cross waves (see Figure 3), i.e. the model was
moored in a soft spring system and irregular long-crested
seas were approaching the vessel from 135° or 225° or both.
In order to check the validity of the superposition
principle with respect to the mean drift forces, tests were
carried out in three phases, i.e. (1) one test to measure
mean drift forces in irregular seas from 135°, (2) one test
in waves from 2250 and (3) one test in irregular cross seas
consisting of a superposition of both irregular wave trains.
Before treating the test results, it is of interest to
check the superposition principle with respect to the
undis-turbed wave elevation at the centre of gravity of the
ves-sel.
The spectra of the long-crested, uni-directional wave
trains generated from either of the two basin sides are
shown in Figure 11. In Figure 12 the calculated sum of the
individual spectra are compared with the spectra obtained
from the wave elevation records measured in irregular cross
-41-using inderendent random wave generator control signals. The
agreement shows that the superposition principle holds very
well for the undisturbed wave trains.
The test duration for tests in irregular seas
corre-sponded to 90 minutes full scale.
The mean wave drift forces on the tanker measured in
the various irregular long-crested, uni-directional seas
along with calculated data are given in Table 7.
In general the measured and calculated mean surge and
sway forces and are in good agreement. For spectrum 1,
the calculated mean surge force is some 30% below the
mea-sured value. The reason for this difference is not clear at
this time. In general differences in the forces are less
than 10%.
The difference between the calculated and measured mean
yaw moments appear to be larger. It should be remembered, however, that the mean yaw moment is derived from the
dif-ference in the mean transverse forces measured fore and aft.
The moment arm amounted to about 320 m for the full scale vessel. The mean yaw moments are therefore rather small in
terms of transverse forces applied at the fore and aft ends. In Table 8 the measured mean forces in irregular cross seas are presented together with calculated data obtained by adding the mean values measured in irregular uni-directional seas, and calculated data obtained by adding calculated data for irregular uni-directional seas.
The calculated mean forces for irregular
uni-direc-tional seas were obtained based on equation (3.17), using
the measured uni-directionl wave spectra presented in Figure
11. The transfer function
P(w,U3,,)
was given again, basedon 3-D diffraction calculations and on equation (3.1). See,
for example, Table 5 for surge force F.
The results shown in Table 8, in general, show that the
superposition principle holds very well for the mean wave
drift forces in irregular cross seas.
In general, the data calculated based on 3-D
diffrac-tion theory also are in good agreement except for those
tests involving spectrum 1. In those cases, diffraction cal-culations underestimate the mean surge force to some
X
extent. This is in agreement with the results given in Table
-43-7. SUMMARY AND CONCLUS IONS
In this paper, some aspects of the general theory
re-garding mean and low frequency second order drift forces in
irregular directional seas were discussed. It was shown
that, given the bi-directional and bi-frequency dependent
quadratic transfer function for the wave drift forces1 the
mean forces and spectral density of the slowly varying part
of the forces could be computed using the directional wave
spectrum as description for the sea condition.
This frequency domain representation, although very useful, is not entirely complete however, since strictly
speaking information should also be given on the
distribu-tion of low frequency forces. The general problem of the
distribution of the second order drift forces in irregular
long-crested seas has been treated among others in ref. [18] and [19], to which the reader is referred.
Time domain representations of drift forces in
direc-tional seas through direct summation of Fourier components
or through the application of the second order term of a
Functional Polynomial have been discussed. In both cases it
was assumed that the wave field consists of a sum of
long-crested irregular wave trains from a number of discrete
directions. The Functional Polynomial allows a deterministic
comparison to be made between measured and computed drift
force records in irregular cross seas.
This
comparison hasaddressed in more detail in future research.
The results of model tests with a 200,000 DWT tanker in regular cross waves and irregular cross seas have confirmed
theoretical predictions with respect to the applicability of
the superposition principle for the mean wave drift forces
in irregular seas while it has also been shown that
addi-tional drift forces occur through the simultaneous presence
of two regular wave fields. The latter effect can be used to
clarify the theoretically predicted increase in low
frequen-cy excitation due to the interaction of waves approaching a vessel from different directions.
Results have been presented of the comparisons between
drift forces obtained from experiments in regular cross
waves and in irregular cross seas and obtained from
3-dimen-sional diffraction theory calculations. In general, the
computed and measured data are in good agreement. The
com-parison has, for the present, been restricted to the mean
drift forces. In a future phase it is envisaged to carry out
experiments and calculations to check the accuracy of
pre-dictions with respect to the slowly varying part of the
-45-REFERENCE S
Grancini, G., lovenitti, L.M. and Pastore, P.: "Moored
tanker behaviour in crossed sea. Field experiences and
model tests". Symposium on Description and Modelling of
Directional Seas, Technical University of Denmark,
Copenhagen, 1984.
Marol, P., Römeljng, J.U. and Sand, S.E.:
"Bi-articu-lated mooring tower tested in directional waves".
Symposium on Description and Modelling of Directional
Seas, Technical University of Denmark, Copenhagen, 1984.
Teigen, P.S.: "The response of a TLP in short-crested
waves". Paper No. OTC 4642, Offshore Technology
Con-ference, Houston, 1983.
Marthinsen, T.: "The effect of short-crested seas on
second order forces and motions". International Work-shop on Ship and Platform Motions, Berkeley, 1983.
Van Oortrnerssen, G., Pin]cster, J.A. and Van den Boom, H.J.J.: "Computer simulations as an aid for offshore
operations". WEMT, Paris, 1984.
Wichers, J.E.W. and Van den Boom, H.J.J.: "Simulation
of the behaviour of SPM-moored vessel in irregular
waves, wind and current". Deep Offshore Technology,
Malta, 1983.
Mohn, B. and Fauveau, V.: "Effect of wave-directional-ity on second-order loads induced by set-down". Applied
Mitsuyasu, .: "Directional spectra of
ocean waves in
generation areas. Conference on Directional Wave
Spec-tra Applications, Berkeley, 1981.
Hasselman, K., Dunckel, M. and Ewing, J.A.:
"Direc-tional wave spectra observed during JONSWAP 1973".
Journal of Physical Oceanography, 8, 1264-1280, 1980.
Lambrakos, K.F.: "Marine pipeline dynamic response to
waves from directional wave sepctra". Ocean
Engineer-ing, Vol. 9, No. 4, 1982.
Tucker, M.J., Challenor, P.G. and Carter, D.J.T.:
"Numerical simulation of a random sea: a common error
and its effect upon wave group statistics".
Applied
Ocean Research, Vol. 6, No. 2, 1984.
Pinkster, J.A.: "Numerical modelling of directional
seas". Symposium on Description and Modelling of
Directional Seas. Technical University of
Denmark, Copenhagen, 1984.
Pinkster, J.A.: "Low frequency second order wave
ex-citing forces on floating structures".
N.S.M.B.
Publi-cation No. 650, Wageningen, 1980.
Bowers, E.C.: "Long period oscillation of moored ships
subject to long waves". R.I.N.A., 1975.
Benschop, A.: "The contribution of the second order
potential to low frequency second order wave exciting
forces on vessels". Department of Mathematics,
-47-Dalzell, J.F.: "Application of the Fundamental
Poly-nomial model to the ship added resistance problem".
Eleventh Symposium on Naval Hydrodynamics, University
College, London, 1976.
Gao, H. and Gu, M. "Determination of non-linear drift
force quadratic transfer function and synthesis of
drift force time history". Marintec Offshore China Con-ference, Shanghai, 1983.
Vinje, T.: "On the statistical distribution of second
order forces and motions". International Shipbuilding
Progress, March, 1983.
Langley, R.S.: "The statistics of second order wave
LIST OF TABLES AND FIGURES
Table i : Main particulars and stability data
of loaded 200,000 DWI' tanker
Amplitude of first harmonic of adjusted regular
uni-directional wave components
Quadratic transfer function for the
longi-tudinal force in cross seas Quadratic transfer function
0ijk for the longi-tudinal force in cross seas
Quadratic transfer function
ijkk for the
longi-tudinal force in long-crested seas
Quadratic transfer function for the
longi-tudinal force in long-crested seas
Measured and calculated mean drift forces and
moment in irregular uni-directional seas
Measured and calculated mean drift forces and moment in irregular cross seas
Schematic representation of wind sea and swell
spectrum
Body plan of 200,000 DWT tanker
Schematic representation of set-up of tanker model in Wave and Current Laboratory
Measured mean drift forces and yaw moment and
undisturbed wave height in regular cross waves.
Wave frequency 0.267 rad/s Table 2 Table 3 : Table 4 Table 5 : Table 6 : Table 7 : Table 8 : Figure 1 : Figure 2 : Figure 3 Figure 4
-49-Measured mean drift forces and yaw moment and undisturbed wave height in regular cross waves. Wave frequency 0.443 radIs
Measured mean drift forces and yaw moment and undisturbed wave height in regular cross waves. Wave frequency 0.713 rad/s
Measured mean drift forces and yaw moment and undisturbed wave height in regular cross waves. Wave frequency 0.887 rad/s
Amplitude and phase angle of mean longitudinal drift force due to interaction effects in
regu-lar cross waves
Amplitude and phase angle of mean transverse drift force due to interaction effects in regu-lar cross waves
Amplitude and phase angle of mean yaw drift moment due to interaction effects in regular cross waves
Spectra of adjusted uni-directional irregular
seas
Spectra of irregular cross seas: Comparison of measured results with results calculated from
superposition of uni-directional irregular seas
Figure 5 : Figure 6 : Figure 7 : Figure 8 : Figure 9 Figure 10 : Figure 11 : Figure 12 :
Table i
Main particulars and stability data of loaded 200,000 DWT tanker
Designation Symbol Unit
Magnitude
Length between perpendiculars m
310.00 Breadth B m 47.17 Depth H m 29.60 Draft fore TF m 18.90 Draft mean TM m 18.90 Draft aft TA m 18.90 Displacement weight tf 240,697 Block coefficient CB - 0.850
Midship section ceofficient
CM - 0.995
Waterplane coefficient C - 0.868
Centre of buoyancy forward of
section 10 FE m 6.61
Centre of gravity above keel m
13.32
Metacentric height GM m 5.78
Radius of gyration in air:
- transverse m 14.77 - longitudinal rn 77.47 - vertical m 79.30
-51-Table 2
Amplitude of first harmonic of adjusted
regular uni-directional wave components
Wave frequency
Wave from Wave from
in rad/s
east side south side Amplitude of first harmonic
mm
(2250) (135°) 0.267 1 .90 i . 94 0.443 1 . 88 i . 90 0.713 i . 99 2.02 0.887 1.82 1 .87Table 3
Quadratic transfer function
for the longitudinal force
in cross seas + Wi + 0.2 0.3 0.4 0.5 0.6 0.7 0.8 0.9 1.0 0.2 0 -7 -11 -9 0 0 0 0 0 0.3 -7 1 -4 -8 -5 0 0 0 0 0.4 -11 -4 -5 -10 -6 5 0 0 0 0.5 -9 -8 -10 -11 -7 6 8 0 0 0.6 0 -5 -6 -7 -9 -2 8 5 0 0.7 0 0 5 6 -2 -10 -1 10 12 0.8 0 0 0 8 8 -1 -7 4 15 0.9 0 0 0 0 5 10 4 -6 -4 1.0 0 0 0 0 0 12 15 -4 -25
Table 4
Quadratic transfer function
for the longitudinal force
in cross seas 0.4 -38 17 0
E
E E E -1 ijk 0.5 0.6 0.7 0.8 0.9 1.0 -29 0 0 0 0 0 -26 -21 0 0 0 0 -15 -21 -19 0 0 0 = 135° 6 o = 225° i. + 0.2 0.3 Wi + 0.2 0 -31 0.3 30 0 0.4 38 17 o.s 29Table 5
Quadratic transfer function
ijkk
for the longitudinal
force in long-crested seas w. + WI 4 0.2 0.3 0.4 0.5 0.6 0.7 0.8 0.9 1.0 0.2 0.3 0.4 0.5 0.6 0.7 0.8 0.9 1.0 0 0 -23 -51 0 0 0 0 0 0 0 -4 -21 -26 0 0 0 0 -23 -4 -10 -14 -17 -7 0 0 0 -51 -21 -14 -20 -12 -6 2 0 0 0 -26 -17 -12 -13 -6 -4 7 0 0 0 -7 -6 -6 -12 -8 0 20 0 0 0 2 -4 -8 -10 -3 12 0 0 0 0 7 0 -3 -10 -11 0 0 0 0 0 20 12 -11 -31
Table 6
Quadratic transfer function
for the longitudinal force
in long-crested seas + Wi + 0.2 0.3 0.4 0.5 0.6 0.7 0.8 0.9 1.0 0.2 0 -146 -166 -116 0 0 0 0 0 0.3 146 0 -81 -90 -45 0 0 0 0 0.4 166 81 0 -50 -50 -17 0 0 0 = 135° 0.5 116 90 50 0 -35 -37 4 0 0 0.6 0 45 50 35 0 -32 -19 23 0 = 135° 0.7 0 0 17 37 32 0 -29 -4 28 0.9 0 0 0 -4 19 29 0 -27 1 in 0.9 0 0 0 0 -23 4 27 0 -30 1.0 0 0 0 0 0 -28 -1 30 0
Table 7
Measured and calculated
mean drift forces and
moment in irregular uni-directional seas Spectrum 1 Spectrum 2 Spectrum 3 M e a n (225°) (225°) (135°) forces Unit and flea- Calcu- Mea- Calcu- Mea- Calcu-morne nt sured lated sured lated sured lated y tf -75.7 -53.0 -16.9 -16.6 -16.9 -18.1 tf -286.5 -293.2 -98.2 -107.5 93.5 112.6 tfm -4685 -3489 -582 -471 1608 600
Table 8
Measured and calculated mean drift forces and moment in irregular cross seas
Calculated Calculated Calculated Calculated Measured Measured (1) (2) (1) (2) tf -98.6 -71.1 -92.6 -84.4 -56.3 -80.6 X tf -195.8 -180.6 -193.0 -277.6 -275.3 -271.1 y tfm -3242 -2889 -3077 -4745 -3234 -3671
Calculated (1): Sum of calculated values given in Table 7 Calculated (2): Sum of measured values given in Table 7
Spectrum 2 (225°) + Spectrum 2 (225°) + + Spectrum 3 (135°) + Spectrum 4 (135°) Mean Spectrum 1 (225°) + Spectrum 1 (225°) + forces + Spectrum 3 (135°) + Spectrum 4 (135°) and Unit moment Calculated Calculated Calculated Calculated Measured (1) (2) Measured (1) (2) tf -32.8 -34.7 -33.8 -18.4 -19.9 -21.8 X tf 0.6 5.1 -4.7 -88.1 -89.6 -82.8 y tfm 708 129 1026 -294 -216 432
w
Figure 1 : Schematic representation of wina sea and swell
BOO'r PLAN
AZT SIDE
SriJTH SIDE
'o
Figure 3 : Schematic representation of set-up of tanker
model in Wave and Current Laboratory
EX
WAVES 225 og
ORCE TRASOUCER WAVES .3S
10400 200
2a
in rn Fx F in ti -200 -400 PHASE -61-20000 10000 0 M in tin, -10000 -20000 120 240 350ANGLE BETWEEN WAVE GENERATORS
n degrees
Figure 4 : Measured mean drift forces and yaw moment and
undisturbed wave height in regular cross waves. Wave frequency 0.267 rad/s
2a N WAV( FREQUENCY
5
/
O.27 r/-
-a----.-,-
N F "1!/
/
/
_-.-*__
0 o20000 10000 o Mg ñ) UrTI 10000 -400 -20000 0 120 240 360
PHASE ANGLE BETWEEN WAVE GENERATORS
in aegrs
Figure 5 : Measured bean drift forces and yaw moment and
undisturbed wave height in regular cross waves. Wave frequency 0.443 rad/s
a WAVE FRE0UElC' 0443 r/3 ,A
/i
B S--/\
1/
/\\
\\//
I, /
/
\.S / / I I / //
lo 400 5 200 2Ça in m o o F F ri ti -200-400
o
P NA SE
-63-120 240 360
ANGLE BETWEEN WAVE GENERATORS
in degreEs 20000 10 000 o M in ttm -10 000 -20 000
Figure 6 : Measured thean drift forces and yaw moment and
undisturbed wave height in regular cross waves. Wave frequency 0.713 rad/s
N
WAVE FREQUEHC'r O713 r/
/
/
\
/
//
//
/
---i---/f
\//
/
/
// I 400 10 5 2002a
in ni 0 0 x y ¡n tf -20010 5 2 o F F u-i tf -200 -400 0 120 240 360
PHASE ANGLE BETWEEN WAVE GENERATORS
in degrees
Figure 7 : Measured bean drift forces and yaw moment and
undisturbed wave height in regular cross waves. Wave frequency 0.887 rad/s
400 .200 0-20000 10000 o M n tim 10000 20000
y
WAVE FRLJECY _--.--,.-. \ 0.657 r/i u'/
/
\
\
----/
20 10 o -65-400 200
Figure 8 : Amplitude and phase angle of mean longitudinal
drift force due to interaction effects in regular cross waves -CALCULATED PIEASURED o o o o s
.
e tS 05 1.0 w 'nc\J z o 10 50 o 400 200
Figure 9 : Amplitude and phase angle of mean transverse
drift force due to interaction effects in regular cross waves CALCULATED .1EASURED
-
o D Q o l-5 05 10 W in rad/s4000 2000 E o I o -67-CALCULATED P4EASURED o o o o o
C..
10 1. W inFigure 10 Amplitudè and phase angle of mean yaw drift
moment due to interaction effects in regular cross waves 400 200 t, C LL o
7. 3 ac To o 'Q 'j-, o w 3 o
Figure 11 : Spectra f adjusted uni-directional irregular
seas 22 SPWrRT.)-4 i n, s i WAVE SPECTWJ.4 2 22 GÇ lOT ?fl Y, WAVE SPCTRJ..r T35 øn.ç. 315 r,, n, 3 WAVE S T35 wy, rRTWT 05. 1.52e" ti.o s
E0
3
o
-69-- .,
Figure 12 : Spectra f irregular cross seas: Comparison of
measured results wjtl-i results calculated from superposition of uni-directional irregular seS
o o E o 3 2O SPCTPtJ,l SPECTRt4 - CM.OA.ATW 1 (22E 3 (135 O.ç) L5 s--s .çi c, s --VECL»4 scas
SCUM4 (1351 (22E o.c)
. sas e_ns ) Y c.,, Y -te s CTRS4 CTPt).4