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648 2012,24(5):648-657 DOI: 10.1016/S1001-6058(11)60288-6 HYDRODYNAMIC INTERACTION BETWEEN FLNG VESSEL AND LNG CARRIER IN SIDE BY SIDE CONFIGURATION* ZHAO Wen-hua, YANG Jian-min, HU Zhi-qiang State Key Laboratory of Ocean Engineering, Shanghai Jiao Tong University, Shanghai 200240, China, E-mail: zwzldh@163.com (Received March 14, 2012, Revised April 23, 2012) Abstract: The Floating Liquefied Natural Gas (FLNG) is a new type of floating platform for the exploitation of stranded offshore oil/gas fields. The side by side configuration for the FLNG vessel and the LNG carrier arranged in parallel is one of the possible choices for the LNG offloading. During the offloading operations, the multiple floating bodies would have very complex responses due to their hydrodynamic interactions. In this study, numerical simulations of multiple floating bodies in close proximity in the side by side offloading configuration are carried out with the time domain coupled analysis code SIMO. Hydrodynamic interactions between the floating bodies and the mechanical coupling effects between the floating bodies and their connection systems are included in the coupled analysis model. To clarify the hydrodynamic effects of the two vessels, numerical simulations under the same environmental condition are also conducted without considering the hydrodynamic interactions, for comparison. It is shown that the hydrodynamic interactions play an important role in the low frequency motion responses of the two vessels, but have little effect on the wave frequency motion responses. In addition, the comparison results also show that the hydrodynamic interactions can affect the loads on the connection systems. Key words: Floating Liquefied Natural Gas (FLNG), hydrodynamic interactions, side by side operation, relative motions Introduction� Due to the high oil prices and the steep increase in the natural gas demand triggered by Japanese nuclear disaster, the stranded offshore gas fields, which were considered not quite favorable projects in the past, are becoming more and more attractive. To exploit those offshore gas fields effectively and eco- nomically, the Floating Liquefied Natural Gas (FLNG), as a new concept of offshore unit, was pro- posed recently. The configurations of an FLNG vessel and an LNG carrier in side by side or tandem arrange- ments are two possible ways of the LNG offloading operation. In the case of the side by side configuration, the FLNG vessel and the LNG carrier are moored in * Project supported by the China National Scientific and Technology Major Project (Grant No. 2011ZX05026-006-05), the Science Foundation of Science and Technology Commi- ssion of Shanghai Municipality (Grant No. 11ZR1417800). Biography: ZHAO Wen-hua (1986-), Male, Ph. D. Candidate Corresponding author: YANG Jian-min, E-mail: jmyang@sjtu.edu.cn close proximity. Therefore, the hydrodynamic intera- ctions between the two vessels can not be ignored. The hydrodynamic interactions might significantly affect the motion responses of the vessels and make the relative motions of the multiple bodies very com- plex. Furthermore, the investigation of the hydrodyna- mic interactions also helps in the prediction of the collision events between the two vessels. The hydrodynamic interactions of multiple floa- ting vessels in the parallel configuration were much studied. In the early studies of multiple bodies, the dynamic cross-coupling among the motions of the bodies and the hydrodynamic interactions between the multiple bodies were not considered. Later, a theory on the hydrodynamic interactions of parallel floating bodies based on a two-dimensional diffraction theory, was proposed. However, an unphysical phenomenon exists in the numerical simulations based on the pote- ntial theory due to the fluid resonant response in the gap of the multiple bodies. Buchner et al.[1] introduced a rigid lid on the free surface within the multi-body diffraction analysis to suppress the unrealistic reso- nant wave oscillations, which is an improvement over 649 the previous methods. Using the same measure to deal with the resonant wave oscillations, Naciri[2] carried out extensive time domain analyses of the side-by-side moored vessels and verified the simulation results through model tests. Pauw et al.[3] considered two ships in a side by side arrangement and replaced the rigid lid with a numerical damping lid. They sugge- sted that the damping parameter should be adjusted in such a way that the drift forces rather than the linear quantities are optimal with respect to the model tests. In order to avoid the restriction that each interacting body must be far enough apart from the other bodies, Kashiwagi and Shi[4] solved the integral equation of the diffraction potential by the Higher-Oder Boundary Element Method (HOBEM). They found that the sma- ller the separation distance between bodies, the larger deviation of the pressure distribution obtained based on the wave interaction theory will be, as compared with the correct results. Lu et al.[5] investigated the dependence of the wave forces of multiple bodies in close proximity on the incident wave frequency, the gap width, the body draft, the body breadth and the body number, based on both the viscous fluid and the potential flow models. Their numerical models were validated by the available experimental data of the fluid oscillation in narrow gaps. Inoue and Kamruzzaman[6] calculated the hydrodynamic radia- tion and the diffraction forces using a three-dimen- sional sink-source technique. In their study, the non- linear connecting and mooring forces were included. Chitrapu et al.[7] evaluated the sea keeping and maneu- vering performances of proximate vessels that are advancing forward using an efficient time domain method. In their study, the non-linear effects of moo- ring lines and fenders and the effects of viscous roll damping were included. Lee et al.[8] calculated the motions of two floating bodies in shallow water. They suggested that the shallow water effects be included in the analysis of floaters in shallow water. Kristiansen and Faltinsen[9] studied the coupled resonant response of a ship and a fixed terminal. One of their conclu- sions is that the linear theory over-predicts the piston- mode amplitude near the resonance, point about three times as compared with the measured value. A compa- rison of the hydrodynamic interactions between single and multi-body responses was made by Yu et al.[10]. They observed significant differences between the res- ponses in single and multi-body cases. Although the multi-body system was much stu- died, data accumulated are still far from enough for safe offloading operations in the side by side configu- ration in real sea states. In this study, a coupled ana- lysis model of the multi-body problem is built, taking into account the hydrodynamic interactions between the two vessels and the mechanical couplings between vessels, mooring systems, hawsers and fenders. Numerical simulations of the multi-body system under a given sea state are carried out with the help of the state-of-the-art code SIMO, the reliability of which was validated by Chen et al.[11]. To clarify the effects of the hydrodynamic interactions, numerical simula- tions are conducted ignoring the hydrodynamic intera- ctions, for comparison. The comparison results show that the hydrodynamic interactions play an important role in the low frequency motion responses, but have little effect on the wave frequency motion responses. The hydrodynamic interactions also have a certain effect on the loads acting on the hawsers and fenders. 1. Numericalmodeling The numerical simulation is carried out with the help of the state-of-the-art time domain coupled code SIMO. Based on the potential theory, the hydrodyna- mic coefficients of the vessels in the side by side con- figuration, such as those of the added mass, the pote- ntial damping, the first-order and second-order wave drift forces, are calculated in the frequency domain. In the multi-body modeling, the hydrodynamic intera- ctions of the two floating bodies are also taken into consideration, in the form of coupled added masses and coupled retardation functions. 1.1 Potential flow The potential flows can be described by the Laplace equation in terms of the velocity potential 2 2 2 2 2 2 ( , , , ) ( , , , ) ( , , , )+ + = 0x y z t x y z t x y z t x y z � � �� � � � � � (1) where ( , , , )x y z t� is the velocity potential function of the coordinates x , y and z , and the time t . The velocity potential can be expressed as ( , ,x y� i, ) = Re[ ( , , ) e ]tz t x y z �� � , in which the real part ( , , )x y z� can further be divided into the incident and scattering parts ( , , ) = ( , , ) + ( , , )I Sx y z x y z x y z� � � (2) The scattering parts ( , , )S x y z� can further be divided into the diffraction part ( , , )D x y z� due to the existence of the floating body, and the radiation part ( , , )R x y z� due to the oscillation of the floating body. And thus, Eq.(2) can be expressed as ( , , ) = ( , , ) + ( , , ) + ( , , )I D Rx y z x y z x y z x y z� � � � (3) Each part of the potential in Eq.(3) can be solved under their corresponding boundary conditions[12]. The incident and diffraction potentials would be used 650 to calculate the wave forces acting on the floating bodies. And the radiation potential ( , , )R x y z� would be used to calculate hydrodynamic coefficients such as those of the added masses and the damping forces induced by the oscillation of the floating bodies, 0 ( ) = Re dnmn m S a s n � � � � � � � � � � � �� ( , = 1, 2, , 6)m n � (4) 0 ( ) = Im dnmn m S c s n � � �� � � � � � � � � �� ( , = 1, 2, , 6)m n � (5) where m� represents the induced velocity potential when the floating body is oscillating in direction m with a unit speed. ( )mna � and ( )mnc � means the added mass and the potential damping in direction m induced by the body oscillation in direction n . � is the oscillation frequency, � is the density of the fluid, and 0S is the wet surface of the floating body. 1.2 Rigid body motion The computed frequency-domain hydrodynamic coefficients are used in the time-domain equation expressed by a two-term Volterra series expression via a Kramers-Kronig relation[13]. The motion equa- tions[14,15] in the time-domain coupled analysis for the FLNG vessel or the LNG carrier are formulated as follows � � � � � � � � � �1 2[ + ( )] + + + +M a D D f K� � � �� �� � � � � wave current wind ext 0 [ ( )] = + + + t h t F F F F� �� � � (6) where M is the generalized mass matrix for the ship hull, ( )a � is the added mass matrix at the infinite frequency, K is the hydrostatic restoring stiffness matrix, 1D and 2D are the linear and quadratic damping matrices, respectively. waveF , windF and currentF denote the wave drag force, the wind drag force and the current drag force, respectively. The last item extF represents any other forces (the specified forces and the forces from station-keeping and cou- pling elements, etc.). ( )h � refers to the retardation function matrix, which is related with the influence of the memory effect in the free-surface and can be obtained by the following equation i1( ) = [ ( ) + i ( )]e d 2 th c a �� � � � �� � � � � (7) where c and a are the radiation damping matrix and the added mass matrix obtained from the freque- ncy domain analysis, respectively, and � is the fre- quency. It should be noted that the damping on the vessel from the viscous skin drag and the wave drift damping should also be included in the term 0 [ ( t h t � � � � )] d� � �� in the form of critical damping, because these variants are related to the motion velocity of the vessel. The two parts in Eq.(7) must be opposite in sign for 0� � and identical for 0� � , namely 0 2( ) = ( )cos( )d =h c� � �� � � � � 0 2 ( )sin ( )da� � �� � � � � � (8) It should be noted that the hydrodynamic intera- ction effects on the frequency dependent added mass and the damping forces are included in the coupled added mass and the coupled retardation functions at the infinite frequency. In such a case, the 6×6 matrix [ + ( )]M a � in Eq.(6) should be written as a 12×12 matrix , , , , ( + ( )) ( ( )) ( ( )) ( + ( )) i i i j j i j j M a a a M a � � � � � � � � � � (9) where the indices i and j refer to the FLNG vessel and the LNG carrier, respectively. It should be noted that the term with the same subscript such as ,i i or ,j j is equal to the term in the single body case, and the term with the different subscripts such as ,i j and ,j i represents the effects from the other body. The 6×6 impulse response function matrix [ ( )]h t �� in Eq.(6) should be written as a 12×12 matrix , , , , ( ) ( ) ( ) ( ) i i i j j i j j h t h t h t h t � � � � � � � � � � � � � � (10) Due to the symmetric properties, we can obtain the following equations , ,[ ( )] = [ ( )]i j j ia a� � , , ,( ) = ( )i j j ih t h t� �� � Thus, the coupled motion equation of the two vessels can be expressed as a set of 12 coupled equa- tions[13,16] , , , , ( ( )) ( ( )) ( ( )) ( ( )) ii i i j j i j j j M a a a M a � � ! " � � � � # # " $ % � � � " � � � # # & ' �� �� 1 , 1 , 2 , 2 , 1 , 1 , 2 , 2 , ( ) ( ) ( ) ( ) ( ) ( ) ( ) ( ) ii i i j i i i j j i j j j i j jj D D D D D D D D � � ! � � � � # # " $ % � � � � � � � � # # & ' � � 651 , , , , ( ) ( ) ( ) ( ) i ii i i j j i j j jj K K f K K � � � � ! ! � � # # # # � � " " $ % $ % � � � � # # � � # # & ' & ' � � � , , 0 , , ( ) ( ) d ( ) ( ) t i ii i i j j i j j jj Fh t h t h t h t F � � � � � � � ! � � ! � � # # # # ( $ % $ % � � � � # # � � # # & ' & ' � � � (11) where iF means the forces acting on the FLNG vessel, which is equal to the right hand side of Eq.(6), while jF means the forces on the LNG carrier. In the numerical simulation, the integrations of the motion equations are carried out by using a 3rd-order Runge- Kutta method. 1.3 Connection system The two vessels are connected through 8 hawsers and 4 fenders. The hawsers are modeled as linear springs according to = Tl k ) (12) where l) is the elongation, k is the effective axial stiffness, and T is the hawser tension. The fender is defined as a contact element, which is attached to the FLNG vessel. And the fender plane is on the LNG carrier. The fender plane is defined by a point and a normal vector. The fenders are modeled in the same way as the hawsers, but with a lateral sti- ffness. 2. Description of the side by side configuration The conceptual FLNG system developed by China National Offshore Oil Corporation (CNOOC) and Marine Design and Research Institute of China is selected as a reference. TheLNG carrier has a dis- placement weight of 1.6×105 t in the full loaded con- dition. The main parameters of the two vessels are listed in Table 1. The FLNG system is designed to be located in South China Sea at water depth of 1 500 m and moored by 12 mooring lines attached to an exte- rnal turret. The details of the mooring system are illu- strated in Table 2. The FLNG vessel and the LNG carrier are connected by 8 hawsers and 4 fenders. The axial stiffness of each hawser is set to be 83.57 kN/m, and with a Safe Working Load (SWL) of 796.95 kN (55% of Minimum Breaking Load (MBL) of 1 449 kN). The force-elongation relationship of each fender is nonlinear. The side by side configuration of the FLNG vessel and the LNG carrier is illustrated in Fig.1. The distance between the two vessels is set to be 4 m, which is equal to the length of the fenders. Table 1 Principal Scantlings of the reference FLNG vessel and the LNG carrier Designation FLNG LNG carrier Length over all, oaL (m) 392.00 289.00 Length between perpendiculars, ppL (m) 356.00 278.00 Breadth, B (m) 69.00 43.20 Depth, D (m) 35.70 26.30 Draft, T (m) 13.85 10.05 Displacement, ) (t) 320 804 95 951 Centre of gravity above base, KG (m) 20.553 14.49 Centre of gravity from AP, LCG (m) 171.020 142.04 Radius of roll gyration, xxK (m) 25.35 14.04 Radius of pitch gyration, yyK (m) 91.36 85.13 Radius of yaw gyration, zzK (m) 93.40 86.00 Table 2 Configuration of the mooring lines in prototype Designation Chain Polyester Chain Length (m) 100 4 000 2 000 Diameter (m) 0.127 0.233 0.127 weigh in air (kg/m) 322.93 33.8 322.93 Submerged weight (kg/m) 280.95 7.9 280.95 Axial stiffness (kN/m) 1 214 733 479 000 1 214 733 Minimum breaking load (kN) 14 971 15 696 14 971 Fig.1 The side by side arrangement (not in a correct scale) 652 Fig.2 Comparison of the time series of the low frequency motions of the two vessels with and without considering their hydrodynamic interactions Table 3 Summary of motion statistics of the side-by-side moored FLNG vessel and LNG carrier FLNG LNG carrier Designation Max. Min. Mean Std. Max. Min. Mean Std. With interaction 0.040 –6.190 –2.85 1.04 1.540 –8.690 –3.77 2.41 Surge Without interaction –0.180 –6.620 –2.85 0.90 1.790 –8.920 –4.02 2.45 With interaction 10.20 –11.08 –1.23 6.45 14.22 –10.65 0.06 6.67 Sway Without interaction 10.08 –11.71 –1.53 6.54 13.91 –11.15 –0.09 6.70 With interaction 3.640 –3.050 0.46 1.95 4.500 –3.110 0.67 2.09 Yaw Without interaction 3.670 –2.940 0.54 2.00 4.720 –2.980 0.88 2.26 During the numerical simulation, a parallel sea environment including wave, wind and current app- roaches the multi-body system with the heading of 180o. The random wave component is described by a three-parameter Jonswap spectrum with a significant wave height of 2.5 m, a spectrum peak of 10 s and a peak enhancement factor of 3. A steady flow of wind is assumed and the mean hourly wind speed at the re- ference height of 10 m is 13 m/s. The current velocity near the free surface is 0.81 m/s. 3. Results and discussions Numerical simulations of the side by side moored FLNG vessel and LNG carrier are carried out with and without considering the hydrodynamic interactions between the two floating vessels. Through the compa- rison of the numerical results, the effects of the hydro- 653 dynamic interactions of multiple bodies are revealed. 3.1 Influence on motion responses The hydrodynamic interactions of the multiple bodies have different effects in different motion modes. The 6 degree-of-freedom motions can be cla- ssified into the following two types: the low frequency motions such as surge, sway and yaw, and the wave frequency motions such as heave, roll and pitch. 3.1.1 Low frequency motions Figure 2 shows the time series of the low freque- ncy motions for the FLNG vessel and the LNG carrier in the two cases. As there are few wave frequency components in the low frequency motions, the time series and the statistics of the motion responses, in- stead of the spectrum analysis results, are shown in this section. Fig.3 Comparison of the time series of the relative low fre- quency motions of the two vessels with and without con- sidering their hydrodynamic interactions As can be seen in Fig.2 (where the surge 1( )d , sway 3( )d and yaw 5( )d motions are for FLNG vessel, and the surge 2( )d , sway 4( )d and yaw 6( )d motions are for LNG carrier), the surge motion response of the LNG carrier is much larger than that of the FLNG vessel, while the sway and yaw motions see little difference. An interesting phenomenon as can be seen from Table 3 is that the statistics of the low frequency motions of each floating vessel keep almost the same in the two simulation cases. This means that the hydrodynamic interactions have little effects on the statistics of the motions responses. However, it can also be seen from Fig.2 that the hydrodynamic interactions change the phase of the low frequency motion responses. The hydrodynamic interactions have the most significant effects on the sway motion responses of the two floating vessels. This phenomenon is consistent with the observations by Buncher et al.[1]. It should be noted that the change of the response phase would induce a change of the relative motion responses. The time series of the rela- tive low frequency motions with and without conside- ring the interactions are shown in Fig.3 for compari- son. Table 4 Summary of relative motion statistics of the side- by-side moored FLNG vessel and LNG carrier Designation Max. Min. Mean Std. With interaction 3.51 –4.62 –0.92 2.15Relative surge Without interaction 3.34 –5.12 –1.18 2.27 With interaction 6.09 –0.66 1.29 1.01Relative sway Without interaction 6.05 –0.64 1.44 1.08 With interaction 2.56 –2.28 0.20 0.83Relative yaw Without interaction 2.31 –2.33 0.34 0.95 As shown in Fig.3 (where 1r , 2r and 3r indi- cate the relative surge, sway and yaw motions) and Table 4, the hydrodynamic interactions have a signifi- cant effect on the phase of the relative motion respo- nses, but little effect on the statistics of the relative motion responses. It should be noted that the relative motions are the differences between the motion respo- nses of the LNG carrier and those of the FLNG vessel. And thus, the negative values of the relative sway mo- tions mean that the two vessels move towards each other, and correspondingly, the positive values indi- cate that the two vessels move away from each other. As there are 4 identical fenders with the length of 4 m between the two vessels to prevent collisions, the ne- gative values of the relative sway motions do not ne- cessarily mean collisions of the two vessels. In fact, when the relative distance between the two vessels is smaller than the fender length, the value of the relative 654 sway motion would become negative. Fig.4 Comparison of the power spectrum of the motion respo- nses with and without considering the hydrodynamic in- teractions Fig.5 Zero-order moments of the wave frequency motions 3.1.2 Wave frequency motions As the heave, roll and pitch motions contain rich wave frequency components, the spectrum analysis is carried out for these motions. As a good measure of the response energy, the zero-order moments of the wave frequency motions are calculated as the integra- ted area under the spectral density curve. Fig.6 Spectra of the tensions acting on the typical hawsers Figure 4 shows the power spectrum of the wave frequency motion responses of the two vessels with and without considering their hydrodynamicintera- ctions, where 1S and 2S indicate the power spe- ctrum of heave motions for FLNG vessel and LNG carrier. 3S and 4S indicate the power spectrum of 655 Table 5 The zero-order moments and the peak values of the spectra for the typical hawsers Zero-order moments(kN2) Peak values(kN2s/rad) Serial numbers With Without % With Without % Hawser #1 909.6 714.0 27.4 123.7 58.2 112.7 Hawser #4 2 077.0 1 487.0 39.7 246.8 121.9 102.5 Hawser #5 1 871.0 1 804.0 3.7 229.7 169.9 35.2 Hawser #8 1 559.0 1 133.0 37.6 245.8 121.3 102.6 pitch motions for FLNG vessel and LNG carrier. It should be noted that the roll motion responses of the FLNG vessel are so small that no valuable parameters can be found. And thus, the power spectrums of the roll motion responses are not shown in Fig.4. To clarify the effects of the hydrodynamic interactions on the response energy of the wave frequency motions, the zero-order moments of the heave and pitch mo- tions are plotted in Fig.5, where p indicates the zero-order moment. A comparison of the results with and without the interactions shows that the hydro- dynamic interactions indeed have effects on the wave frequency motions under the given sea state, but not so significantly as those on the low fre- quency mo- tions. 3.2 Influence on connection system In addition to the motion responses of the two vessels, the hydrodynamic interactions can also affect the loads on the connection systems which are related with the relative motion responses of the two vessels. 3.2.1 Hawsers The typical connection hawsers such as hawser #1, hawser #4, hawser #5 and hawser #8 (whose arra- ngements are shown in Fig.1 in Section 2) are selected as the representative cases. As the time series of the hawser forces have rich wave frequency components, the power density function would be a good measure to analyze the hawser responses. And thus, the spe- ctrum analyses are carried out for the time series of the loads acting on the representative hawsers. Figure 6 shows the spectra of the tensions acting on the typical connection hawsers with and without considering the hydrodynamic interactions between the multiple bodies. Figure 6 shows that the conne- ction hawsers in different locations are acted by diffe- rent forces. The loads acting on the hawsers located in the bow of the vessels are much smaller that those in the stern of the vessels. The hawser #4 in the middle section of the vessels is acted by similar loads as those acting on the hawser #5. It can also been from Fig.6 that the spectrum peak frequency of hawser #1 is simi- lar to that of hawser #8, and that the spectrum peak frequency of hawser #4 is similar to that of hawser #5. This means that the spectrum peak frequencies of the hawsers have a close relation with their locations. As can be seen from Fig.6, the hydrodynamic in- teractions have a significant effect on the responses of the hawser forces. Although little effect can be found on the spectrum peak frequencies, the peak values of the spectra increase sharply when the hydrodynamic interactions are included in the simulations (See Table 5). To further show the effects of the hydrodynamic interactions, the zero-order moments, as a good mea- sure of the response energy of the hawser forces, are compared (See Table 5). It is shown that the hydro- dynamic interactions between the multiple bodies would largely increase the response energy of the forces acting on the connection hawsers. As shown in Table 5, the response energy of the forces increases by 27.4% for hawser #1, 39.7% for hawser #4, 3.7% for hawser #5, and 37.6% for hawser #8. Fig.7 Comparison of the time series of the forces acting on the fenders with and without considering the hydrodynamic interactions 3.2.2 Fenders Figure 7 (where 1f and 4f indicate the force acting on Fender #1 and Fender #4, respectively) and Table 6 show the time series and the statistics of the 656 fender forces with and without considering the hydro- dynamic interactions. From Fig.7, it can be seen that the time series of the fender forces are in the form of impulses, which means that there are many collisions between the two vessels. In addition, the fender loca- ted in the bow is acted by larger loads than that in the stern. Figure 7 shows that the hydrodynamic intera- ctions can significantly affect the phase of the force responses. Table 6 shows that the maximum and mean values of the fender forces are slightly affected by the hydrodynamic interactions, but the standard deviation of the Fender #1 changes from 269.3 kN to 375 kN, an increase of 39.4%, due to the effects of the hydro- dynamic interactions. Table 6 Statistics of the fender forces with and without con- sidering the hydrodynamic interactions Designation Max. Min. Mean Std. With interaction 2 914.4 0 115.5 375.4 Fender #1 Without interaction 3 051.5 0 110.5 269.3 With interaction 1 975.3 0 114.1 295.7 Fender #4 Without interaction 1 953.2 0 115.1 290.0 4. Conclusion remarks A numerical model for the multi-body problem is established with consideration of the hydrodynamic interactions between the two floating vessels and the mechanical coupling effects between vessels, mooring systems and connection systems. Hydrodynamic inte- ractions between multiple bodies are investigated through the comparison of the numerical results with and without considering the hydrodynamic intera- ctions. The following conclusions are obtained: (1) The hydrodynamic interactions between mul- tiple bodies can significantly affect the phases of the low frequency motion responses, but have little effect on the frequency motion responses. (2) Due to the existence of the hydrodynamic in- teractions between multiple bodies, the response energy of the loads acting on the hawsers would in- crease. And the largest increase can reach 39.7% under the given condition in this study. (3) Hawsers in different locations would be acted by different loads. Generally, the hawsers in the stern of the vessels would be acted by larger loads than those in the bow of the vessels. (4) The effects of the hydrodynamic interactions on the fender forces are mainly shown in the standard deviation of the force response. 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