# Initiating a Mathematical Model for Prediction of 6-DOF Motion of Planing Crafts in Regular Waves

Authors: Parviz Ghadimi; Abbas Dashtimanesh; Yaser Faghfoor Maghrebi
Journal: International Journal of Engineering Mathematics
 (2013)

---

## Abstract

Nowadays, most of the dynamic research on planing ships has been directed towards analyzing the ships motions in either 3-DOF (degrees of freedom) mode in the longitudinal vertical plane or in 3-DOF or 4-DOF mode in the lateral vertical plane. For this reason, the current authors have started a research program of describing the dynamic behavior of planing ships in a 6-DOF mathematical model. This program includes the developing of a 6-DOF computer simulation program in the time domain. This type of simulation can be used for predicting the response of these planing vessels to the environmental disturbances during high-speed sailing. In this paper, the development of the mathematical model will be presented. Furthermore, a discussion will be offered about the use of these static contributions in a time domain simulation for modeling the behavior of planing crafts in regular waves.


---

## Body

## 1. Introduction

Prediction of planing craft motion is one of the main computational challenges in marine engineering. Due to the involved computational time, computational fluid dynamics is very expensive. Experimental works are also very costly. Therefore, several researchers have tried to present mathematical models which are very easy and economical. In the last decades, two branches of mathematical models have been developed which are in two or three degrees of freedom. First branch was developed by Savitsky [1]. Savitsky’s model has not been developed extensively. For example, it cannot be applied to the planing motion in irregular waves, and it is also difficult to use it to obtain time domain simulation. However, second branch which was developed by Martin [2] has been implemented by many authors. In reality, Martin’s [2] model was in frequency domain. Zarnick [3] worked on this model and performed time domain calculations. Later, Zarnick [4] developed Martin’s model even further for planing craft motion in irregular waves. He compared his results with the experimental findings of Fridsma [5, 6] and found his model to be in favorable agreement with the experimental data. However, Zarnick’s model had some restrictions which had been resolved by some researchers. In fact, after several decades, a model which was initially developed by Zarnick is still a reliable tool for planing craft motion.Keuning [7] extended Zarnick’s [3, 4] model to incorporate a formulation for the sinkage and trim of the ship at high speeds. He also studied the hydrodynamic lift distribution along the length of the ship with nonlinear added mass and wave exciting force in both regular and irregular waves. Hicks et al. [8] expanded the full nonlinear force and moment equations of Zarnick [3, 4] in a multivariable Taylor series. They replaced equations of motion by a set of highly coupled constant-coefficient ordinary  differential equations, valid through third order. Akers [9] summarized the semi-empirical method, three-dimensional panel method, and their advantages and drawbacks dealing with planing hull motion analysis. He reviewed in detail the two-dimensional low aspect ratio strip theory developed by Zarnick [3, 4]. Akers [9] modeled the added mass coefficients based on an empirical formula that is a function of deadrise angle.  Garme and Rosén  [10] presented a similar time domain analysis of simulating a planing hull in head seas, which is different from the classical Zarnick’s model in precalculation scheme of hydrostatic and hydrodynamic coefficients.Later,  Grame and Rosen  [11] improved his model by adding a reduction function based on model tests and published model data for the near-transom pressure. This reduced the pressure near the stem gradually to zero at the stem. van Dayzen [12] extended the original model developed by Zarnick [3, 4] and later extended by Keuning [7] to three degrees of freedom of surge, heave, and pitch motion in both regular and irregular head seas. The simulations can be carried out with either a constant forward speed or constant thrust. He also validated the results by experimental data of two models and found his model very sensitive to the hull geometry. More recently,  Sebastianii et al.  [13] developed previous studies to combine the roll, heave, and pitch degrees of freedom.In the current paper, a mathematical model based on the models of Zarnick [3] and  Sebastianii et al.  [13] is developed. In all previous studies,  2d+t  theory based symmetric wedge water entry has been used. However, the present paper tries to develop a mathematical model based on asymmetric wedge water entry which leads to various forces and moments. Actually, this mathematical model can be considered as a first step in extending Zarnick’s model to six degrees of freedom, and the authors are well aware of the fact that this mathematical model must be gradually modified, step by step.


## 2. Equations of Motions

Planing motions can be divided into two main parts, linear and angular motion. Moreover, various forces and moments including hydrodynamics force, hydrostatic force, weight, and wave effects, must be considered in equations of motion. However, no aerodynamic forces are investigated. Based on Newton’s second law, governing equations of motions can be written as(1)mx¨=Fx(t)=Xr(t)+Xw(t)+Xf(t),my¨=Fy(t)=Yr(t)+Yw(t)+Yf(t),mz¨=Fz(t)=Zr(t)+Zw(t)+Zf(t),IGxxψ¨=Mx(t)=Kr(t)+Kw(t)+Kf(t),IGyyθ¨=My(t)=Pr(t)+Pw(t)+Pf(t),IGzzφ¨=Mz(t)=Rr(t)+Rw(t)+Rf(t),
where subscripts r, w, and f denote hydrostatic,  hydrodynamic,  and wave force and moment. F and M also indicate force and moment while m, I, and t are mass, moment inertia, and time, respectively. Equations (1) are written based on the shown coordinate system. To solve equations of motions, force and moment must be calculated. To calculate force and moment, various theories such as 2d+t, momentum, and added mass theory become necessary.


## 3.2d+t Theory

In a ship-fixed coordinate system,2.5D theory means that the two-dimensional equations are solved together with three-dimensional free surface conditions. If the attention is focused on an Earth-fixed cross-plane, one will see a time-dependent problem in 2D cross-plane, when the vessel is passing through it. Accordingly, the theory is also called 2d+t theory. In an Earth-fixed coordinate system, a prismatic planing vessel of trim angle τ (up to 20 degrees) is moving through an Earth-fixed cross-plane with speed Us, as shown in Figure 1. At time t=t0, the cross-section is just above the free surface; at time t=t1 the cross-section is penetrating the free surface; and at time t=t2, flow separates from the chine line. Therefore, one can see a process where a V-shaped section enters the water surface in this cross-plane by a speed of V=Usτ. However, it must be noted that the developed mathematical model has some limitation, especially at high speed. Trim angle cannot exceed 20 degrees, and the wavelength must also be larger than the hull length.Figure 1
Demonstration of2d+t concept [14].Same procedure can be defined for penetration of an asymmetric wedge into the free surface. This means that side force can also exist. This side force leads to roll moment and yaw moment. Therefore, various motions of planing hull can be taken into account. Based on this definition, two different coordinate systems should be considered (as shown in Figures2 and 3). Generally, three fundamental aspects due to inclination of section which are shown in Figure 4 can be considered [13](i)
Nonsymmetrical action of fluid on boat: the boat in oblique sea undergoes different actions of fluid in its port and starboard side, due to different absolute wave velocities and relative boat motions relevant to roll.(ii)
Nonsymmetry of the section impacting against water: due to roll motion, the section which impacts against water is not symmetrical; starboard and port sides are considered separately with their “equivalent deadrise angle”, which is the resultant of the local geometrical deadrise and the roll angle in order to compute the added mass terms.(iii)
Nonsymmetrical submerged volume geometry: submerged volume and wet surface are no longer symmetrical, affecting hydrostatics and in general force application points.Finally, it is concluded that the force acting on the hull must be calculated section by section for starboard side and port side, separately.Figure 2
Coordinate system 1 [13].Figure 3
Coordinate system 2 [13].Figure 4
Force acting on an inclined wedge [13].


## 4. Regular Wave Theory

In the present computational model, wave forces are obtained by neglecting diffraction forces (only Froude-Krylov forces are considered). It is also assumed that the wave excitation is caused by the instantaneous wetted surface and by the vertical component of the wave orbital velocity at the surfacewz. The influence of the horizontal component of wave orbital velocity on both the horizontal and vertical motions is neglected, because this velocity is considered to be relatively small in comparison with the forward speed of the craft. The normal velocity V and the velocity component parallel to the keel U can be written as functions of the craft's forward speed, heave, pitch, and vertical component of wave orbital velocity [7] as in
(2)U(ζ,ξ)=x˙CG(t)cosθ(t)-[z˙CG(t)-wz(ξ,t)]sinθ(t),V(ξ,t)=x˙CG(t)sinθ(t)-[z˙CG(t)-wz(ξ,t)]×cosθ(t)-θ˙(t)ξ.
For regular waves, the wave elevation of a linear deep water wave [13] is
(3)ξ(x,y,t)=acos(kxcosμ+kysinμ-ωet+ε),
where a is the wave amplitude, k is the wave number, and c is the wave celerity.


## 5. Force Acting on the Hull

As mentioned earlier, the numerical model employed here for prediction of planing motion utilizes a modified2d+t theory with momentum theory. The vessel is considered to be composed of a series of 2D wedges, and the three dimensional problem is subsequently solved as a summation of the individual 2D slices. The forces acting on a cross-section consist of four components (force per unit length): the weight of the section (w), a hydrodynamic lift associated with the change of fluid momentum (fM), a viscous lift force associated with the cross flow drag (fcd) [7, 12], and a buoyancy force associated with instantaneous displaced volume (fb) [3, 12].


### 5.1. Momentum and Added Mass Theories

The hydrodynamic lift force associated with the change of fluid momentum per unit length,fM, acting at a section is [9] as follows:
(4)fM=DDt(maV)=maV˙+Vm˙a-∂∂ξ(maV)dξdt=maV˙+Vm˙a-U∂∂ξ(maV),
where ma is the added mass associated with the section form. U is the relative fluid velocity parallel to the keel, and V is the velocity in plane of the cross-section normal to the baseline. Formula for other mentioned force can be found in most of previous works [3, 4, 7, 12, 13].In subject of hydrodynamics force, port and starboard sides can be considered, separately. This means that(5)fMPT=-DDt(maPTV),fMSB=-DDt(maSBV).
To obtain hydrodynamic force, added mass theory will be implemented. Added mass is a widely used concept in a variety of applications like maneuvering, seakeeping, and planing calculations. The amount of added mass varies according to the shape and size of the body. The added mass for a V-shaped wedge is given by [3]
(6)ma=kaπ2ρb2,
and its time derivative is
(7)dmadt=m˙a=kaπρbb˙,
where ka is the added mass coefficient and b is the instantaneous half beam of the section. Depth of penetration for each section is given by [9]
(8)d=bcotβ,
where β is the deadrise angle. Taking into account the effect of water pileup, the effective depth of penetration (de) is expressed as [9]
(9)de=Cpud,
where Cpu is the pileup or splash-up coefficient. Overall, it can be written that [9]
(10)b=decotβ=Cpudcotβ.
Hence, it can be concluded  that  the time derivative of the added mass is
(11)m˙a=kaπρb(Cpucotβ)d˙.
Therefore, when the immersion exceeds the chine, we have [9]
(12)ma=kaπ2ρbmax2=cte,m˙a=0,
where bmax is the half beam at chine. Furthermore, at any point P(ξ,ζ), it can be written [7]  as
(13)x(t)=xCG(t)+ξcosθ(t)+ζsinθ(t),z(t)=zCG(t)-ξsinθ(t)+ζcosθ(t).
The submergence of a section in terms of the motion will be as follows [7]:
(14)h(ξ,ζ,t)=ZCG(t)-η(ξ,t)=ZCG(t)-ξsinθ(t)+ζcosθ(t)-r(ξ,t).
For wavelengths which are long, in comparison to the draft, and for small wave slopes, the immersion of a section measured perpendicular to the baseline is approximated as in [7]
(15)d≈h(ξ,ζ,t)cosθ(t)-vsinθ(t),
where v is the wave slope. The rate change of submergence is given by [7]
(16)d˙=z˙-η˙cosθ-vsinθ+z-η(cosθ-vsinθ)2∂(cosθ-νsinθ)∂t.
Since the immersion z-η is always small in the valid range, the relationship can be further simplified to
(17)d˙≈z˙-η˙cosθ-vsinθ.
Consequently,
(18)m˙a≈kaπρb(Cpucotβ)z˙-η˙cosθ-vsinθ.


### 5.2. Total Hydrodynamic Force and Moment

The total hydrodynamic forces acting on the vessel are obtained by integrating sectional2D forces over the wetted length, lw, of the craft. Force and moments in each direction are presented, separately.


#### 5.2.1. Horizontal Force

The force acting in the horizontalx-direction is given by
(19)Fx=-(∫lfMsinθdξ+∫lfCDsinθdξ)cosψ=-(∫l(NMP+NMS)sinθdξ+∫l(fCDP+fCDS)sinθdξ)×cosψ=-(∫l(DDt(maPVP)+DDt(maSVS))sinθdξ+∫l(fCDP+fCDS)sinθdξ)cosψ=-[∫l(US∂∂ξ(maSVS)maPV˙P+maSV˙S+m˙aPVP+m˙aSVS-UP∂∂ξ(maPVP)-US∂∂ξ(maSVS))dξ+∫l(CDρ(bPVP2+bSVS2))dξ]sinθcosψ,
where
(20)V˙=x¨CGsinθ-θ¨ξ+z¨CGcosθ-w˙zcosθ+θ˙(x˙CGcosθ-z˙CGsinθ)+wzθ˙sinθ,∂U∂ξ=∂wz∂ξsinθ,∂V∂ξ=-θ˙-∂wz∂ξcosθ,dwzdt=w˙z-U∂wz∂ξ.
By substituting (20) in (19), horizontal force will be as follows:
(21)Fx=-[∫l(US∂∂ξmaP(x¨CGsinθ-θ¨ξ+z¨CGcosθ-w˙zPcosθ+θ˙(x˙CGcosθ-z˙CGsinθ)+wzPθ˙sinθ)+maS(x¨CGsinθ-θ¨ξ+z¨CGcosθ-w˙zScosθ+θ˙(x˙CGcosθ-z˙CGsinθ)+wzSθ˙sinθ)+m˙aPVP-UP∂∂ξ(maPVP)+m˙aSVS-US∂∂ξ(maSVS))dξ+∫l(CDρ(bPVP2+bSVS2))dξ]sinθcosψ=-[∫lmaPdξx¨CGsinθ-θ¨∫lmaPξdξ+∫lmaPdξz¨CGcosθ+∫lmaP(dwzPdt+U∂wzP∂ξ)×cosθdξ+∫lmaPθ˙(x˙CGcosθ-z˙CGsinθ)dξ+∫lmaPwzPθ˙sinθdξ+∫lm˙aPVPdξ+UPVPmaP|bowstern-∫lmaPVP∂UP∂ξdξ+∫lCDρbPVP2dξ+{SimilarSterms}∫lmaPdξ]sinθcosψ.
Now, the following definitions will be introduced:
(22)Ma=∫lmadξ,Qa=∫lmaξdξ,
and subsequently,
(23)Fx=-[∫lCDρbPVP2Max¨CGsin2θcosψ-Qaθ¨sinθcosψ+Maz¨CGcosθsinθcosψ+∫lmaP(dwzPdt+U∂wzP∂ξ)cosθdξsinθcosψ+Maθ˙(x˙CGcosθ-z˙CGsinθ)sinθcosψ+∫lmaPwzPθ˙sinθdξsinθcosψ+∫lm˙aPVPdξsinθcosψ+UPVPmaP|bowsternsinθcosψ-∫lmaPVP∂UP∂ξdξsinθcosψ+∫lCDρbPVP2dξsinθcosψ+{SimilarSterms}].


#### 5.2.2. Side Force

Similar to the horizontal force, lateral force can also be obtained. Side force is a result of the difference between side force at port and starboard of the craft which yield sway motion. Generally, it can be written as follows:(24)Fy=(∫lfMdξ+∫lfCDdξ)sinψcosθ=(∫l(NMP-NMS)dξ±∫l(fCDP-fCDS)dξ)sinψcosθ=(∫l(DDt(maPVP)-DDt(maSVS))dξ±∫l(fCDP-fCDS)dξ)sinψcosθ=[∫l(US∂∂ξ(maSVS)maPV˙P-maSV˙S+m˙aPVP-m˙aSVS-UP∂∂ξ(maPVP)+US∂∂ξ(maSVS))dξ+∫l(CDρ(bPVP2-bSVS2))dξ]sinψcosθ.
Using (20), the side force will be equal to
(25)FY=[∫l(US∂∂ξ(maSVS)maP(x¨CGsinθ-θ¨ξ+z¨CGcosθ-w˙zPcosθ+θ˙(x˙CGcosθ-z˙CGsinθ)+wzPθ˙sinθ)-maS(x¨CGsinθ-θ¨ξ+z¨CGcosθ-w˙zScosθ+θ˙(x˙CGcosθ-z˙CGsinθ)+wzSθ˙sinθ)+m˙aPVP-UP∂∂ξ(maPVP)-m˙aSVS+US∂∂ξ(maSVS))dξ+∫l(CDρ(bPVP2-bSVS2))dξ]cosθsinψ.
Finally, one can write
(26)Fy=[MaPx¨CGsinθ-θ¨QaP+MaPz¨CGcosθ+∫lmaP(dwzPdt+U∂wzP∂ξ)cosθdξ+MaPθ˙(x˙CGcosθ-z˙CGsinθ)+∫lmaPwzPθ˙sinθdξ+∫lm˙aPVPdξ+UPVPmaP|bowstern-∫lmaPVP∂UP∂ξdξ+∫lCDρbPVP2dξ-{SimilarSterms}θ¨QaP]cosθsinψ.


#### 5.2.3. Vertical Force

Same as other forces, vertical force will be as follows:(27)Fz=(∫lfMdξ-∫lfCDdξ)cosψcosθ-∫lfBdξ=(∫l(NMP+NMS)dξ-∫l(fCDP+fCDS)dξ)×cosψcosθ-∫laBFρgAdξ=(∫l(DDt(maPVP)+DDt(maSVS))dξ-∫l(fCDP+fCDS)dξ(DDt(maPVP)+DDt(maSVS)))cosψcosθ-∫laBFρgAdξ=-[∫l(US∂∂ξ(maSVS)maPV˙P+maSV˙S+m˙aPVP+m˙aSVS-UP∂∂ξ(maPVP)-US∂∂ξ(maSVS))dξ+∫l(CDρ(bPVP2+bSVS2))dξ]cosψcosθ-∫laBFρgAdξ.
Again, using (20), we have
(28)Fz=[∫lCDρbPVP2-MaPx¨CGsinθ+QaPθ¨-MaPz¨CGcosθ+∫lmaP(dwzPdt+U∂wzP∂ξ)cosθdξ-MaPθ˙(x˙CGcosθ-z˙CGsinθ)-∫lmaPwzPθ˙sinθdξ-∫lm˙aPVPdξ+UPVPmaP|bowstern-∫lmaPVP∂UP∂ξdξ-∫lCDρbPVP2dξ+{SimilarSterms}]×cosθsinψ-∫laBFρgAdξ.


#### 5.2.4. Roll Moment

When all the hydrodynamics forces are determined, it can be an easy task to compute various moments acting on the hull. Roll moment (Mx) is due to side and vertical forces which can be considered as follows:
(29)Mx=Fyzc+Fzyc,
where zc and yc are the distance from CG to center of action for side and vertical forces, successively, which can easily be calculated.


#### 5.2.5. Pitch Moment

Pitch moment can also be computed similar to roll moment. However, there exist two ways for pitch moment calculation. In the first method, it is enough to act similar to the roll moment. This means that(30)My=Fzxc,
where xc is the horizontal distance from CG to center of action for vertical force. In the second method, we can integrate sectional 2D moments over the wetted length I of the craft as follows:
(31)My=[∫lCDρbPVP2ξQaPx¨CGsinθ-IaPθ¨+QaPz¨CGcosθ-∫lmaP(dwzPdt+U∂wzP∂ξ)cosθξdξ-QaPθ˙(x˙CGcosθ-z˙CGsinθ)+∫lmaPwzPθ˙sinθξdξ+∫lm˙aPVPξdξ+UPVPmaPξ|stern+∫lmaPVP∂wzP∂ξsinθξdξ+∫lCDρbPVP2ξdξ+{SimilarSterms}]·cosψ-∫laBFρgAcosθξdξ.


#### 5.2.6. Yaw Moment

Yaw moment is as follows:(32)Mz=Fyxc,
where xc is the horizontal distance from CG to center of action for the side force. Now, equations of motion can be solved to determine the time domain motions of the planing hull.


## 5.1. Momentum and Added Mass Theories

The hydrodynamic lift force associated with the change of fluid momentum per unit length,fM, acting at a section is [9] as follows:
(4)fM=DDt(maV)=maV˙+Vm˙a-∂∂ξ(maV)dξdt=maV˙+Vm˙a-U∂∂ξ(maV),
where ma is the added mass associated with the section form. U is the relative fluid velocity parallel to the keel, and V is the velocity in plane of the cross-section normal to the baseline. Formula for other mentioned force can be found in most of previous works [3, 4, 7, 12, 13].In subject of hydrodynamics force, port and starboard sides can be considered, separately. This means that(5)fMPT=-DDt(maPTV),fMSB=-DDt(maSBV).
To obtain hydrodynamic force, added mass theory will be implemented. Added mass is a widely used concept in a variety of applications like maneuvering, seakeeping, and planing calculations. The amount of added mass varies according to the shape and size of the body. The added mass for a V-shaped wedge is given by [3]
(6)ma=kaπ2ρb2,
and its time derivative is
(7)dmadt=m˙a=kaπρbb˙,
where ka is the added mass coefficient and b is the instantaneous half beam of the section. Depth of penetration for each section is given by [9]
(8)d=bcotβ,
where β is the deadrise angle. Taking into account the effect of water pileup, the effective depth of penetration (de) is expressed as [9]
(9)de=Cpud,
where Cpu is the pileup or splash-up coefficient. Overall, it can be written that [9]
(10)b=decotβ=Cpudcotβ.
Hence, it can be concluded  that  the time derivative of the added mass is
(11)m˙a=kaπρb(Cpucotβ)d˙.
Therefore, when the immersion exceeds the chine, we have [9]
(12)ma=kaπ2ρbmax2=cte,m˙a=0,
where bmax is the half beam at chine. Furthermore, at any point P(ξ,ζ), it can be written [7]  as
(13)x(t)=xCG(t)+ξcosθ(t)+ζsinθ(t),z(t)=zCG(t)-ξsinθ(t)+ζcosθ(t).
The submergence of a section in terms of the motion will be as follows [7]:
(14)h(ξ,ζ,t)=ZCG(t)-η(ξ,t)=ZCG(t)-ξsinθ(t)+ζcosθ(t)-r(ξ,t).
For wavelengths which are long, in comparison to the draft, and for small wave slopes, the immersion of a section measured perpendicular to the baseline is approximated as in [7]
(15)d≈h(ξ,ζ,t)cosθ(t)-vsinθ(t),
where v is the wave slope. The rate change of submergence is given by [7]
(16)d˙=z˙-η˙cosθ-vsinθ+z-η(cosθ-vsinθ)2∂(cosθ-νsinθ)∂t.
Since the immersion z-η is always small in the valid range, the relationship can be further simplified to
(17)d˙≈z˙-η˙cosθ-vsinθ.
Consequently,
(18)m˙a≈kaπρb(Cpucotβ)z˙-η˙cosθ-vsinθ.


## 5.2. Total Hydrodynamic Force and Moment

The total hydrodynamic forces acting on the vessel are obtained by integrating sectional2D forces over the wetted length, lw, of the craft. Force and moments in each direction are presented, separately.


### 5.2.1. Horizontal Force

The force acting in the horizontalx-direction is given by
(19)Fx=-(∫lfMsinθdξ+∫lfCDsinθdξ)cosψ=-(∫l(NMP+NMS)sinθdξ+∫l(fCDP+fCDS)sinθdξ)×cosψ=-(∫l(DDt(maPVP)+DDt(maSVS))sinθdξ+∫l(fCDP+fCDS)sinθdξ)cosψ=-[∫l(US∂∂ξ(maSVS)maPV˙P+maSV˙S+m˙aPVP+m˙aSVS-UP∂∂ξ(maPVP)-US∂∂ξ(maSVS))dξ+∫l(CDρ(bPVP2+bSVS2))dξ]sinθcosψ,
where
(20)V˙=x¨CGsinθ-θ¨ξ+z¨CGcosθ-w˙zcosθ+θ˙(x˙CGcosθ-z˙CGsinθ)+wzθ˙sinθ,∂U∂ξ=∂wz∂ξsinθ,∂V∂ξ=-θ˙-∂wz∂ξcosθ,dwzdt=w˙z-U∂wz∂ξ.
By substituting (20) in (19), horizontal force will be as follows:
(21)Fx=-[∫l(US∂∂ξmaP(x¨CGsinθ-θ¨ξ+z¨CGcosθ-w˙zPcosθ+θ˙(x˙CGcosθ-z˙CGsinθ)+wzPθ˙sinθ)+maS(x¨CGsinθ-θ¨ξ+z¨CGcosθ-w˙zScosθ+θ˙(x˙CGcosθ-z˙CGsinθ)+wzSθ˙sinθ)+m˙aPVP-UP∂∂ξ(maPVP)+m˙aSVS-US∂∂ξ(maSVS))dξ+∫l(CDρ(bPVP2+bSVS2))dξ]sinθcosψ=-[∫lmaPdξx¨CGsinθ-θ¨∫lmaPξdξ+∫lmaPdξz¨CGcosθ+∫lmaP(dwzPdt+U∂wzP∂ξ)×cosθdξ+∫lmaPθ˙(x˙CGcosθ-z˙CGsinθ)dξ+∫lmaPwzPθ˙sinθdξ+∫lm˙aPVPdξ+UPVPmaP|bowstern-∫lmaPVP∂UP∂ξdξ+∫lCDρbPVP2dξ+{SimilarSterms}∫lmaPdξ]sinθcosψ.
Now, the following definitions will be introduced:
(22)Ma=∫lmadξ,Qa=∫lmaξdξ,
and subsequently,
(23)Fx=-[∫lCDρbPVP2Max¨CGsin2θcosψ-Qaθ¨sinθcosψ+Maz¨CGcosθsinθcosψ+∫lmaP(dwzPdt+U∂wzP∂ξ)cosθdξsinθcosψ+Maθ˙(x˙CGcosθ-z˙CGsinθ)sinθcosψ+∫lmaPwzPθ˙sinθdξsinθcosψ+∫lm˙aPVPdξsinθcosψ+UPVPmaP|bowsternsinθcosψ-∫lmaPVP∂UP∂ξdξsinθcosψ+∫lCDρbPVP2dξsinθcosψ+{SimilarSterms}].


### 5.2.2. Side Force

Similar to the horizontal force, lateral force can also be obtained. Side force is a result of the difference between side force at port and starboard of the craft which yield sway motion. Generally, it can be written as follows:(24)Fy=(∫lfMdξ+∫lfCDdξ)sinψcosθ=(∫l(NMP-NMS)dξ±∫l(fCDP-fCDS)dξ)sinψcosθ=(∫l(DDt(maPVP)-DDt(maSVS))dξ±∫l(fCDP-fCDS)dξ)sinψcosθ=[∫l(US∂∂ξ(maSVS)maPV˙P-maSV˙S+m˙aPVP-m˙aSVS-UP∂∂ξ(maPVP)+US∂∂ξ(maSVS))dξ+∫l(CDρ(bPVP2-bSVS2))dξ]sinψcosθ.
Using (20), the side force will be equal to
(25)FY=[∫l(US∂∂ξ(maSVS)maP(x¨CGsinθ-θ¨ξ+z¨CGcosθ-w˙zPcosθ+θ˙(x˙CGcosθ-z˙CGsinθ)+wzPθ˙sinθ)-maS(x¨CGsinθ-θ¨ξ+z¨CGcosθ-w˙zScosθ+θ˙(x˙CGcosθ-z˙CGsinθ)+wzSθ˙sinθ)+m˙aPVP-UP∂∂ξ(maPVP)-m˙aSVS+US∂∂ξ(maSVS))dξ+∫l(CDρ(bPVP2-bSVS2))dξ]cosθsinψ.
Finally, one can write
(26)Fy=[MaPx¨CGsinθ-θ¨QaP+MaPz¨CGcosθ+∫lmaP(dwzPdt+U∂wzP∂ξ)cosθdξ+MaPθ˙(x˙CGcosθ-z˙CGsinθ)+∫lmaPwzPθ˙sinθdξ+∫lm˙aPVPdξ+UPVPmaP|bowstern-∫lmaPVP∂UP∂ξdξ+∫lCDρbPVP2dξ-{SimilarSterms}θ¨QaP]cosθsinψ.


### 5.2.3. Vertical Force

Same as other forces, vertical force will be as follows:(27)Fz=(∫lfMdξ-∫lfCDdξ)cosψcosθ-∫lfBdξ=(∫l(NMP+NMS)dξ-∫l(fCDP+fCDS)dξ)×cosψcosθ-∫laBFρgAdξ=(∫l(DDt(maPVP)+DDt(maSVS))dξ-∫l(fCDP+fCDS)dξ(DDt(maPVP)+DDt(maSVS)))cosψcosθ-∫laBFρgAdξ=-[∫l(US∂∂ξ(maSVS)maPV˙P+maSV˙S+m˙aPVP+m˙aSVS-UP∂∂ξ(maPVP)-US∂∂ξ(maSVS))dξ+∫l(CDρ(bPVP2+bSVS2))dξ]cosψcosθ-∫laBFρgAdξ.
Again, using (20), we have
(28)Fz=[∫lCDρbPVP2-MaPx¨CGsinθ+QaPθ¨-MaPz¨CGcosθ+∫lmaP(dwzPdt+U∂wzP∂ξ)cosθdξ-MaPθ˙(x˙CGcosθ-z˙CGsinθ)-∫lmaPwzPθ˙sinθdξ-∫lm˙aPVPdξ+UPVPmaP|bowstern-∫lmaPVP∂UP∂ξdξ-∫lCDρbPVP2dξ+{SimilarSterms}]×cosθsinψ-∫laBFρgAdξ.


### 5.2.4. Roll Moment

When all the hydrodynamics forces are determined, it can be an easy task to compute various moments acting on the hull. Roll moment (Mx) is due to side and vertical forces which can be considered as follows:
(29)Mx=Fyzc+Fzyc,
where zc and yc are the distance from CG to center of action for side and vertical forces, successively, which can easily be calculated.


### 5.2.5. Pitch Moment

Pitch moment can also be computed similar to roll moment. However, there exist two ways for pitch moment calculation. In the first method, it is enough to act similar to the roll moment. This means that(30)My=Fzxc,
where xc is the horizontal distance from CG to center of action for vertical force. In the second method, we can integrate sectional 2D moments over the wetted length I of the craft as follows:
(31)My=[∫lCDρbPVP2ξQaPx¨CGsinθ-IaPθ¨+QaPz¨CGcosθ-∫lmaP(dwzPdt+U∂wzP∂ξ)cosθξdξ-QaPθ˙(x˙CGcosθ-z˙CGsinθ)+∫lmaPwzPθ˙sinθξdξ+∫lm˙aPVPξdξ+UPVPmaPξ|stern+∫lmaPVP∂wzP∂ξsinθξdξ+∫lCDρbPVP2ξdξ+{SimilarSterms}]·cosψ-∫laBFρgAcosθξdξ.


### 5.2.6. Yaw Moment

Yaw moment is as follows:(32)Mz=Fyxc,
where xc is the horizontal distance from CG to center of action for the side force. Now, equations of motion can be solved to determine the time domain motions of the planing hull.


## 5.2.1. Horizontal Force

The force acting in the horizontalx-direction is given by
(19)Fx=-(∫lfMsinθdξ+∫lfCDsinθdξ)cosψ=-(∫l(NMP+NMS)sinθdξ+∫l(fCDP+fCDS)sinθdξ)×cosψ=-(∫l(DDt(maPVP)+DDt(maSVS))sinθdξ+∫l(fCDP+fCDS)sinθdξ)cosψ=-[∫l(US∂∂ξ(maSVS)maPV˙P+maSV˙S+m˙aPVP+m˙aSVS-UP∂∂ξ(maPVP)-US∂∂ξ(maSVS))dξ+∫l(CDρ(bPVP2+bSVS2))dξ]sinθcosψ,
where
(20)V˙=x¨CGsinθ-θ¨ξ+z¨CGcosθ-w˙zcosθ+θ˙(x˙CGcosθ-z˙CGsinθ)+wzθ˙sinθ,∂U∂ξ=∂wz∂ξsinθ,∂V∂ξ=-θ˙-∂wz∂ξcosθ,dwzdt=w˙z-U∂wz∂ξ.
By substituting (20) in (19), horizontal force will be as follows:
(21)Fx=-[∫l(US∂∂ξmaP(x¨CGsinθ-θ¨ξ+z¨CGcosθ-w˙zPcosθ+θ˙(x˙CGcosθ-z˙CGsinθ)+wzPθ˙sinθ)+maS(x¨CGsinθ-θ¨ξ+z¨CGcosθ-w˙zScosθ+θ˙(x˙CGcosθ-z˙CGsinθ)+wzSθ˙sinθ)+m˙aPVP-UP∂∂ξ(maPVP)+m˙aSVS-US∂∂ξ(maSVS))dξ+∫l(CDρ(bPVP2+bSVS2))dξ]sinθcosψ=-[∫lmaPdξx¨CGsinθ-θ¨∫lmaPξdξ+∫lmaPdξz¨CGcosθ+∫lmaP(dwzPdt+U∂wzP∂ξ)×cosθdξ+∫lmaPθ˙(x˙CGcosθ-z˙CGsinθ)dξ+∫lmaPwzPθ˙sinθdξ+∫lm˙aPVPdξ+UPVPmaP|bowstern-∫lmaPVP∂UP∂ξdξ+∫lCDρbPVP2dξ+{SimilarSterms}∫lmaPdξ]sinθcosψ.
Now, the following definitions will be introduced:
(22)Ma=∫lmadξ,Qa=∫lmaξdξ,
and subsequently,
(23)Fx=-[∫lCDρbPVP2Max¨CGsin2θcosψ-Qaθ¨sinθcosψ+Maz¨CGcosθsinθcosψ+∫lmaP(dwzPdt+U∂wzP∂ξ)cosθdξsinθcosψ+Maθ˙(x˙CGcosθ-z˙CGsinθ)sinθcosψ+∫lmaPwzPθ˙sinθdξsinθcosψ+∫lm˙aPVPdξsinθcosψ+UPVPmaP|bowsternsinθcosψ-∫lmaPVP∂UP∂ξdξsinθcosψ+∫lCDρbPVP2dξsinθcosψ+{SimilarSterms}].


## 5.2.2. Side Force

Similar to the horizontal force, lateral force can also be obtained. Side force is a result of the difference between side force at port and starboard of the craft which yield sway motion. Generally, it can be written as follows:(24)Fy=(∫lfMdξ+∫lfCDdξ)sinψcosθ=(∫l(NMP-NMS)dξ±∫l(fCDP-fCDS)dξ)sinψcosθ=(∫l(DDt(maPVP)-DDt(maSVS))dξ±∫l(fCDP-fCDS)dξ)sinψcosθ=[∫l(US∂∂ξ(maSVS)maPV˙P-maSV˙S+m˙aPVP-m˙aSVS-UP∂∂ξ(maPVP)+US∂∂ξ(maSVS))dξ+∫l(CDρ(bPVP2-bSVS2))dξ]sinψcosθ.
Using (20), the side force will be equal to
(25)FY=[∫l(US∂∂ξ(maSVS)maP(x¨CGsinθ-θ¨ξ+z¨CGcosθ-w˙zPcosθ+θ˙(x˙CGcosθ-z˙CGsinθ)+wzPθ˙sinθ)-maS(x¨CGsinθ-θ¨ξ+z¨CGcosθ-w˙zScosθ+θ˙(x˙CGcosθ-z˙CGsinθ)+wzSθ˙sinθ)+m˙aPVP-UP∂∂ξ(maPVP)-m˙aSVS+US∂∂ξ(maSVS))dξ+∫l(CDρ(bPVP2-bSVS2))dξ]cosθsinψ.
Finally, one can write
(26)Fy=[MaPx¨CGsinθ-θ¨QaP+MaPz¨CGcosθ+∫lmaP(dwzPdt+U∂wzP∂ξ)cosθdξ+MaPθ˙(x˙CGcosθ-z˙CGsinθ)+∫lmaPwzPθ˙sinθdξ+∫lm˙aPVPdξ+UPVPmaP|bowstern-∫lmaPVP∂UP∂ξdξ+∫lCDρbPVP2dξ-{SimilarSterms}θ¨QaP]cosθsinψ.


## 5.2.3. Vertical Force

Same as other forces, vertical force will be as follows:(27)Fz=(∫lfMdξ-∫lfCDdξ)cosψcosθ-∫lfBdξ=(∫l(NMP+NMS)dξ-∫l(fCDP+fCDS)dξ)×cosψcosθ-∫laBFρgAdξ=(∫l(DDt(maPVP)+DDt(maSVS))dξ-∫l(fCDP+fCDS)dξ(DDt(maPVP)+DDt(maSVS)))cosψcosθ-∫laBFρgAdξ=-[∫l(US∂∂ξ(maSVS)maPV˙P+maSV˙S+m˙aPVP+m˙aSVS-UP∂∂ξ(maPVP)-US∂∂ξ(maSVS))dξ+∫l(CDρ(bPVP2+bSVS2))dξ]cosψcosθ-∫laBFρgAdξ.
Again, using (20), we have
(28)Fz=[∫lCDρbPVP2-MaPx¨CGsinθ+QaPθ¨-MaPz¨CGcosθ+∫lmaP(dwzPdt+U∂wzP∂ξ)cosθdξ-MaPθ˙(x˙CGcosθ-z˙CGsinθ)-∫lmaPwzPθ˙sinθdξ-∫lm˙aPVPdξ+UPVPmaP|bowstern-∫lmaPVP∂UP∂ξdξ-∫lCDρbPVP2dξ+{SimilarSterms}]×cosθsinψ-∫laBFρgAdξ.


## 5.2.4. Roll Moment

When all the hydrodynamics forces are determined, it can be an easy task to compute various moments acting on the hull. Roll moment (Mx) is due to side and vertical forces which can be considered as follows:
(29)Mx=Fyzc+Fzyc,
where zc and yc are the distance from CG to center of action for side and vertical forces, successively, which can easily be calculated.


## 5.2.5. Pitch Moment

Pitch moment can also be computed similar to roll moment. However, there exist two ways for pitch moment calculation. In the first method, it is enough to act similar to the roll moment. This means that(30)My=Fzxc,
where xc is the horizontal distance from CG to center of action for vertical force. In the second method, we can integrate sectional 2D moments over the wetted length I of the craft as follows:
(31)My=[∫lCDρbPVP2ξQaPx¨CGsinθ-IaPθ¨+QaPz¨CGcosθ-∫lmaP(dwzPdt+U∂wzP∂ξ)cosθξdξ-QaPθ˙(x˙CGcosθ-z˙CGsinθ)+∫lmaPwzPθ˙sinθξdξ+∫lm˙aPVPξdξ+UPVPmaPξ|stern+∫lmaPVP∂wzP∂ξsinθξdξ+∫lCDρbPVP2ξdξ+{SimilarSterms}]·cosψ-∫laBFρgAcosθξdξ.


## 5.2.6. Yaw Moment

Yaw moment is as follows:(32)Mz=Fyxc,
where xc is the horizontal distance from CG to center of action for the side force. Now, equations of motion can be solved to determine the time domain motions of the planing hull.


## 6. Solution of Equations of Motion

The solution of the derived equations of motion is complicated. They form a set of three coupled second-order nonlinear differential equations which has to be solved using standard numerical techniques in the time domain. The set of equations is first transformed into a set of six coupled first-order nonlinear differential equations by introducing a state vector. Subsequently, resulting equations must be solved using a numerical method such as Runge-Kutta-Merson.Knowing the initial state variables at time instantt0, the equations are simultaneously solved for the small time increment Δt to yield the solution at t+Δt. The advantage of the Runge-Kutta-Merson method is that it is high order and it has adaptive step size control. More details can be found in many reference books like [15].


## 7. Validation

It must be denoted that, based on our knowledge, there is no experimental or numerical work on planing motion in 6 degrees of freedom. Therefore, to validate the developed mathematical model, it is reasonable to examine the basis of the developed code. For this purpose, experiments of Fridsma [5] are considered. He used a prismatic hull with 10, 20, and 30 deadrise  angles  in his experiments (Figure 5). Moreover, characteristics of the hull which is considered in the current study are presented in Table 1. To validate the current solutions, planing motion at both calm water and regular wave will be compared against the experiments. At first, resistance of the ship hull at calm water is obtained and compared against experiments of Fridsma, and then planing motion at regular wave for eighteen different cases is investigated at different wavelength and wave height which are presented in Table 2.Table 1
Characteristics of the considered prismatic hull.
Model
A
B
L
/
b
5
5
β (deg)
20
20
LCG (%L)
59
62
τ (deg)
4
4
V/√L
4
6
C
Δ
0.608
0.608Table 2
Wave characteristics for eighteen different cases.
Run conditions
No.
H/b
λ/L
h/H
1
0.111
1
0.18
2
0.167
1
0.17
3
0.222
1
0.17
4
0.056
2
0.93
5
0.111
2
0.84
6
0.167
2
0.81
7
0.167
2
0.74
8
0.222
2
0.73
9
0.334
2
0.59
10
0.334
2
0.61
11
0.111
3
1.18
12
0.222
3
1.13
13
0.334
3
1.05
14
0.111
4
1.23
15
0.222
4
1.11
16
0.334
4
1.07
17
0.111
6
1.04
18
0.334
6
0.97Figure 5
Prismatic hull.In addition to some details like the designated parameters in Table2, more details should be considered to perform simulations. For example, ship hull is divided into 76 sections, and initial conditions are adopted based on [3, 5]. Figure 6 indicates that numerical details which are adopted in 2d+t simulations are completely in good agreement with the physical characteristics of the problem. In fact, the obtained resistance from 2d+t solutions is in excellent agreement with the experimental data. Therefore, it can be concluded that the considered setting may be suitable for future regular wave solutions.Figure 6
Hull resistance at calm water.Furthermore, Figure7 shows the obtained results for the heave and pitch motions at different H/B ratios. Details of the considered variables are reported in Table 2. It is observed that for wavelength equal to the ship length, the obtained results are not accurate, and an over prediction is seen. However, by increasing the wavelength, the results are more accurate. This can be attributed to the assumption that the wavelength must be sufficiently larger than the ship length. This assumption has been utilized in all previous studies. Overall, it can be concluded that the current mathematical model can be implemented for practical design of planing hulls seakeeping. However, it is worth mentioning that there is urgency for measuring planing craft motions (6-DOF) at regular and irregular waves as a benchmark case.Comparison of heave and pitch motions with experiments of Fridsma [5].
(a)
(b)
(c)
(d)
(e)


## 8. Results

After validation, it is necessary to study the planing craft motion in six degrees of freedom in regular waves. For this purpose, cases 15 and 17 in Table2 are considered. Ship hull is divided to 76 sections and initial condition for each degree of freedom is arbitrarily adopted. These initial values can be identified using the presented results. Moreover, three initial roll angles 0, 5, and 10 degrees are compared against each other. This means that H and λ are kept fixed (cases 15 and 17), and effects of an initial roll angle on planing craft motion are studied. Initial yaw and sway values are also kept to be zero. It must be mentioned that the main purpose of these simulations is the examination of the developed mathematical model.The obtained results are shown in Figures8 and 9. Figure 8 shows the results related to case 15. First, roll angle is set to zero. No sway or yaw motion occurs. This is due to the fact that there is no asymmetric force which can lead to yaw moment and sway motion. Therefore, heave and pitch motions and vertical acceleration will be regular.Effects of roll angle on planing craft motions for case 15.
(a)
Zero degree roll angle
(b)
Five degrees roll angle
(c)
Ten degrees roll angleEffects of roll angle on planing craft motions for case 17.
(a)
Zero degree roll angle
(b)
Five degrees roll angle
(c)
Ten degrees roll angleAfterward, an initial roll equal to 5 degrees is examined. Initial conditions are the same as in the previous case except for the roll angle. It is observed that the roll angle is damped after 8 seconds and again increased. This leads to irregular behavior of heave and pitch in regular wave condition. Yaw and sway of planing hull are also increased by time. These results can be analyzed by the fact that damping force acts on the roll motion and decreases it. However, due to the asymmetric fluid flow in roll motion, some yaw moment and sway force are generated, and regular wave force causes a severe increase in sway and yaw motions. Consequently, roll motion will also be intensified. Due to these behaviors, irregular heave and pitch motions exist.When roll angle is increased to 10 degrees, a similar behavior can be seen too. However, magnitudes of planing motions are different. It is observed that roll motion is relatively damped at 3 until 5 seconds. At the same time, heave and pitch motions remain constant, and, consequently, vertical accelerations due to water impact phenomenon are omitted. However, encounter wave acts on the hull and leads to a new roll angle. In the meantime, yaw and sway motions increase at a relatively constant rate.In addition to case 15, case 17 (Table2) is also considered with the same methodology. Initial roll angle is defined, and it is observed that at zero roll angle, planing hull has a regular behavior. It is clearly seen that no sway and yaw motions are created and that the presented mathematical model works appropriately. As expected, bow acceleration is also larger than the CG acceleration. It is due to this fact that main water entry phenomenon occurs at the fore part of the hull.At 5 degrees roll angle, after 8 seconds, roll is damped and heave of the hull is increased, and, consequently, pitch motion is relatively damped. However, roll motion is affected by the encounter wave and is thus intensified. Moreover, due to the wave effects and unsteady roll motion, sway and yaw continue by a constant rate. Finally, it must be mentioned that variation of surge velocity is not yet completely modeled, and must be considered in the next version of the developed code.In the last part of case 17, roll angle of 10 degrees is considered. Similar behavior relative to the third part of case 15 can be observed. In a range of time, roll is damped, and as a result, heave, pitch, and acceleration become constant. Further studies must be performed for understanding these physics.


## 9. Conclusions

In this paper, various theories of momentum, added mass and2d+t theories are implemented to develop a mathematical model for simulation of six degrees of freedom motion of a planing craft in regular waves. Therefore, 2d+t theory is developed for asymmetric wedge water entry, and a set of formulas is derived for computation of various forces and moments on planing hulls. Solution of equations of motions is also considered by a well-known numerical method Runge-Kutta-Merson which controls the time step size efficiently.In the absence of any six degrees computational data or experiments for planing craft motions, it was decided to validate the present model by using Fridsma’s experiment in regular waves for heave and pitch motions. Comparisons indicate that the developed code can model planing motion reasonably accurate. Furthermore, to demonstrate the model capability for six degrees of freedom computations, Fridsma model is considered and effort was made to study the planing hull behavior at the initial roll angles. Three roll angles including 0, 5, and 10 degrees are considered, and the behavior of the planing hull is studied. It is observed that for different wave conditions, similar behavior is observed at similar roll angles. Moreover, due to the roll motion, an intensive sway motion may occur. Irregular heave and pitch motions are also generated due to the asymmetric effect of the roll motion and the encounter wave. These simulations show the reasonable behavior of the developed mathematical model. It must be mentioned that variation of surge velocity is not completely modeled yet and will be considered in the next version of the developed code. Moreover, some experimental studies should be conducted to further develop or modify the presented mathematical model.



---

*Source: 853793-2013-08-19.xml*