Artificial Equilibrium Points in the Low-Thrust Restricted Three-Body Problem When Both the Primaries Are Oblate Spheroids

Amit Mittal¹, Krishan Pal²

¹Department of Mathematics, A.R.S.D College, University of Delhi, New Delhi, India.
²Department of Mathematics, Maharaja Agrasen College, University of Delhi, New Delhi, India.

DOI: 10.4236/ijaa.2018.84028                

Abstract

This paper studies the existence and stability of the artificial equilibrium points (AEPs) in the low-thrust restricted three-body problem when both the primaries are oblate spheroids. The artificial equilibrium points (AEPs) are generated by canceling the gravitational and centrifugal forces with continuous low-thrust at a non-equilibrium point. Some graphical investigations are shown for the effects of the relative parameters which characterized the locations of the AEPs. Also, the numerical values of AEPs have been calculated. The positions of these AEPs will depend not only also on magnitude and directions of low-thrust acceleration. The linear stability of the AEPs has been investigated. We have determined the stability regions in the xy, xz and yz-planes and studied the effect of oblateness parameters A₁(0<A₁<1) and  A₂(0<A₂<1) on the motion of the spacecraft. We have found that the stability regions reduce around both the primaries for the increasing values of oblateness of the primaries. Finally, we have plotted the zero velocity curves to determine the possible regions of motion of the spacecraft.

Keywords

Restricted Three-Body Problem, Artificial Equilibrium Points, Low-Thrust, Stability, Oblate Spheroid, Zero Velocity Curves

1. Introduction

Generally, the restricted three-body problem is one of the most important problem in the field of celestial mechanics. In the Restricted Three-Body Problem (R3BP), the mass of the third body (i.e., the spacecraft) is assumed to be negligible in comparison to the two more massive bodies, defined as the primary and the secondary. It is assumed that the two primaries revolving in circular orbits about their common center of mass, known as the barycenter. It is then possible to model the motion of the spacecraft in a frame of reference that rotates about the barycenter at the same rotation rate as the two primaries. The motion of the spacecraft is affected by the motion of the primaries but not affect them. To study the motion of the third body is known as restricted three-body problem. There are five equilibrium points in the classical restricted three-body problem (R3BP), three of them are on the straight line joining the primaries, called collinear equilibrium points, and two of them setup equilateral triangle with the primaries. The collinear equilibrium points $L_{\mathrm{1,2,3}}$ are always unstable in the linear sense for any value of mass parameter $\mu$ whereas the triangular points $L_{\mathrm{4,5}}$ are stable if $\mu <{\mu }_c=0.03852\cdots$ . Szebehely [1] . Many perturbing forces, like oblateness, radiation forces of the primaries, Coriolis and centrifugal forces etc., have been included in the study of the R3BP. Many results have been published to the study in the restricted three-body problem with effect of oblateness; see Subbarao and Sharma [2] , Bhatnagar and Chawla [3] , Tsirogiannis et al. [4] , Mittal et al. [5] , Singh [6] , Beevi and Sharma [7] , Abouelmagd [8] , Jain and Aggarwal [9] . Zotos [10] has determined the basins of attraction associated with the equilibrium points in the planar CR3BP where one of the primary bodies is an oblate spheroid or an emitter of radiation. Also, he has noticed that the structure of the basins of convergence is more affected by the mass ratio and radiation pressure parameters than the oblateness parameter. Srivastava et al. [11] have introduced Kustaanheimo-Stiefel (KS)-transformation to reduce the order of singularities arising due to the motion of an infinitesimal body in the vicinity of smaller primary in the R3BP when the bigger primary is a source of radiation and smaller one as an oblate spheroid. They have found that KS-regularization reduces the order of the pole from five to three at the point of singularity of the governing equations of motion.

The new equilibrium points can be generated if the continuous constant acceleration uses by a spacecraft to balance the gravitational and centrifugal forces. These points are usually referred to Artificial Equilibrium Points (AEPs). Recently, low-thrust propulsion systems as solar-sail and the electric propulsion are being developed not only for controlling satellite orbit, but also as main engines for interplanetary transfer orbits. These low-thrust propulsion systems are able to provide continuous control acceleration to the spacecraft and thus, increase mission design flexibility. Farquhar [12] has studied the concept of telecommunication systems using equilibrium points and investigated ballistic periodic orbits about these points in the Earth-Moon system. Dusek [13] , McInnes et al. [14] , Broschart and Scheeres [15] have studied the stability of equilibrium points with continuous control acceleration. Morimoto et al. [16] have studied the existence and stability of the AEPs in the low-thrust R3BP and found the stable regions. They have used the discriminant of cubic equation and the Descartes sign rule to study the stability of these AEPs. Baig and McInnes [17] have investigated the artificial three-body equilibria for hybrid low-thrust propulsion. In their study, they have introduced a new concept of creating AEPs in the R3BP when the third body uses a hybrid of solar-sail and electric propulsion. Further, there are many precise work related to the low-thrust restricted three-body problem; see Bombardelli and Pelaez [18] , Aliasi et al. [19] [20] , Ranjana and Kumar [21] , Yang et al. [22] , Lei and Xu [23] . Bu et al. [24] have investigated the positions and dynamical characteristic of AEPs in a binary asteroid system with continuous low-thrust. They have found the stable regions of AEPs by a parametric analysis and studied the effect of the mass ratio and ellipsoid parameters on the stable region. Further, they have analyzed the effect of the continuous low-thrust on the feasible region of motion by ZVCs.

In the present work, we have focussed on the study of the motion of the spacecraft in the low-thrust restricted three-body problem when both the primaries are oblate spheroids. Here, we have extended the work of Morimoto et al. [16] . We have arranged the present work as follows: In Secttion 2, we have derived the equations of motion of the spacecraft. In Secttion 3, we have found the locations of the AEPs. In Secttion 4, we have determined the linear stability. In Secttion 5, we have computed the zero velocity curves. Finally, in Secttion 6, we have concluded the results obtained.

2. Equations of Motion

In this section, we shall determine the equations of motion of the spacecraft in the low-thrust restricted three-body problem when both the primaries are oblate spheroids. Suppose two bodies of masses m₁ and m₂ $\left(m_1>m_2\right)$ are the primaries moving with angular velocity $\omega$ in circular orbits about their center of mass O taken as origin, and let the infinitesimal body (spacecraft) of mass m₃ be also moving in the plane of motion of m₁ and m₂. The motion of the spacecraft is affected by the motion of m₁ and m₂ but not affect them. The line joining the primaries m₁ and m₂ is taken as X-axis and the line passes through the origin O and perpendicular to the X-axis and lying in the plane of motion of m₁ and m₂ is considered as Y-axis, the line which passes through the origin and perpendicular to the plane of motion of the primaries is taken as Z-axis. In a synodic frame, the system of synodic coordinates $O\left(xyz\right)$ , initially coincident with the system of inertial coordinates $O\left(XYZ\right)$ , rotating with the angular velocity $\omega$ about Z-axis; (the z axis is coincident with Z-axis). Let the primaries of masses m₁ and m₂ be located at $\left(-\mu \mathrm{,0,0}\right)$ and $\left(1-\mu \mathrm{,0,0}\right)$ respectively and the spacecraft be located at the point $\left(x\mathrm{,}y\mathrm{,}z\right)$ (see Figure 1). The angular

velocity of the primaries is given by the relation $\omega =\sqrt{\frac{G\left(m_1+m_2\right)}{l^3}}$ , where l is

distance between the primaries, and G is Gravitational constant. We scale the units by taking the sum of the masses and the distance between the primaries

both equal to unity. Therefore $m_1=1-\mu$ , $m_2=\mu$ and $\mu =\frac{m_2}{m_1+m_2}$ with

Figure 1. Configuration of the problem.

$m_1+m_2=1$ . Also, the scale of the time is chosen so that the gravitational constant is unity. Let $a_1\mathrm{,}{b}_1\mathrm{,}{c}_1$ and $a_2\mathrm{,}{b}_2\mathrm{,}{c}_2$ are the semi axes of rigid bodies of masses m₁ and m₂ respectively. The equation of motion of the spacecraft in vector form is expressed as

$\frac{{\text{d}}^{2}r}{\text{d}{t}^2}+2w\times \frac{\text{d}r}{\text{d}t}=a-\nabla \Omega =F,$ (1)

where $\Omega$ is the potential (McCuskey [25] ) of the system that combines the gravitational potential and the potential from the centripetal acceleration which is defined as

$\Omega =-\frac{n^2}{2}\left(x^2+y^2\right)-\frac{1-\mu }{r_1}-\frac{\mu }{r_2}-\frac{\left(1-\mu \right)A_1}{2r_1^3}-\frac{\mu A_2}{2r_2^3},$

and

$F$ = total force acting on m₃ = $F_1+F_2$ ,

$F_1$ = Gravitational force exerted on m₃ due to m₁ along m₃m₁,

$F_2$ = Gravitational force exerted on m₃ due to m₂ along m₃m₂.

The vector $a=\left(a_x,a_y,a_z\right)$ is low-thrust acceleration and $r={\left(x,y,z\right)}^{\text{T}}$ is the position vector of the spacecraft from the origin. Thus, the equations of motion of the spacecraft with continuous low-thrust in dimensionless co-ordinate system can be written as Morimoto et al. [16]

$\begin{array}{l}\ddot{x}-2n\stackrel{\dot{}}{y}=-{\Omega }_x+a_x=-{\Omega }_x^{*},\\ \ddot{y}+2n\stackrel{\dot{}}{x}=-{\Omega }_y+a_y=-{\Omega }_y^{*},\\ \ddot{z}=-{\Omega }_z+a_z=-{\Omega }_z^{*},\end{array}\}$ (2)

where ${\Omega }^{\mathrm{<mo>\; *\; </mo>}}$ is the effective potential of the system with continuous low-thrust can be written as

$\begin{array}{c}{\Omega }^{*}=\Omega -a_{x}x-a_{y}y-a_{z}z\\ =-\frac{n^2}{2}\left(x^2+y^2\right)-\frac{1-\mu }{r_1}-\frac{\mu }{r_2}-\frac{\left(1-\mu \right)A_1}{2r_1^3}-\frac{\mu A_2}{2r_2^3}-a_{x}x-a_{y}y-a_{z}z,\end{array}$

where

$r_1=\sqrt{{\left(x+\mu \right)}^2+y^2+z^2},$

$r_2=\sqrt{{\left(x+\mu -1\right)}^2+y^2+z^2},$

$a=\sqrt{a_x^2+a_y^2+a_z^2}.$

The required mean motion of the primaries denoted by n, which is given by the relation:

$n^2=1+\frac{3}{2}\left(A_1+A_2\right),$

where A₁ is the oblateness parameter of m₁ which is defined as

$A_1=\frac{a_1^2-c_1^2}{5l^2},0<A_1<1,a_1=b_1\left(a_1>c_1\right)$ , andA₂ is the oblateness parameter of m₂ which is also defined as $A_2=\frac{a_2^2-c_2^2}{5l^2},0<A_2<1,a_2=b_2\left(a_2>c_2\right)$ , where l be the distance between the primaries.

3. Locations of the Artificial Equilibrium Points

In order to find the AEPs of the system, taking velocity and acceleration of the system equal to zero. For obtaining the artificial equilibrium points (AEPs) of the system, we have adopted the similar procedures of McInnes et al. [14] , Morimoto et al. [16] , Baig and McInnes [17] , and Bu et al. [24] in the low-thrust R3BP when both the primaries are oblate spheroid. The AEPs denoted by $\left(x_0\mathrm{,}{y}_0\mathrm{,}{z}_0\right)$ are the solution of the equations given by:

$\begin{array}{l}-n^2{x}_0+\frac{1-\mu }{r_1^3}\left(x_0+\mu \right)\left(1+\frac{3A_1}{2r_1^2}\right)+\frac{\mu }{r_2^3}\left(x_0+\mu -1\right)\left(1+\frac{3A_2}{2r_2^2}\right)-a_x=0,\\ -n^2{y}_0+\frac{1-\mu }{r_1^3}{y}_0\left(1+\frac{3A_1}{2r_1^2}\right)+\frac{\mu }{r_2^3}{y}_0\left(1+\frac{3A_2}{2r_2^2}\right)-a_y=0,\\ \frac{1-\mu }{r_1^3}{z}_0\left(1+\frac{3A_1}{2r_1^2}\right)+\frac{\mu }{r_2^3}{z}_0\left(1+\frac{3A_2}{2r_2^2}\right)-a_z=0.\end{array}\}$ (3)

The control acceleration components $\left(a_x\mathrm{,}{a}_y\mathrm{,}{a}_z\right)$ of an AEP $\left(x_0\mathrm{,}{y}_0\mathrm{,}{z}_0\right)$ are

$a_x=-n^2{x}_0+\frac{1-\mu }{r_1^3}\left(x_0+\mu \right)\left(1+\frac{3A_1}{2r_1^2}\right)+\frac{\mu }{r_2^3}\left(x_0+\mu -1\right)\left(1+\frac{3A_1}{2r_2^2}\right),$

$a_y=-n^2{y}_0+\frac{1-\mu }{r_1^3}{y}_0\left(1+\frac{3A_1}{2r_1^2}\right)+\frac{\mu }{r_2^3}{y}_0\left(1+\frac{3A_2}{2r_2^2}\right),$

$a_z=\frac{1-\mu }{r_1^3}{z}_0\left(1+\frac{3A_1}{2r_1^2}\right)+\frac{\mu }{r_2^3}{z}_0\left(1+\frac{3A_2}{2r_2^2}\right).$

When $A_1=0,A_2=0,a=\left(0,0,0\right)$ , the above Equations (3) reduce to the classical equations obtained by Szebhely [1] . When $A_1=A_2=0$ and $a\ne \left(0,0,0\right)$ , the above Equations (3) reduce to the equations obtained by Morimoto et al. [16] . Solving Equations (3) for $z=0$ , then the AEPs are lie in the xy-plane and obtained by solving ${\Omega }_x^{*}=0,{\Omega }_y^{*}=0$ . We have obtained the five AEPs for given thrust and oblateness parameters denoted by $L_1\mathrm{,}{L}_2\mathrm{,}{L}_3\mathrm{,}{L}_4$ and L₅ as shown in Figure 2.

Figure 2. The locations of the five AEPs in the low-thrust R3BP with the effect of constant control acceleration and oblateness parameters. Panel-(a) for $\mu =0.1$ , $A_1=0.0015$ , $A_2=0.0015$ and for different values of $a=\left(0.0001,0,0\right)\left(\text{gray},\text{red}\right)$ , $\left(\mathrm{0.01,0,0}\right)\left(\text{gray},\text{green}\right)$ , $\left(0.02,0,0\right)\left(\text{gray},\text{magenta}\right)$ , $\left(0.03,0,0\right)\left(\text{gray},\text{orange}\right)$ , and panel-(b) for $\mu =0.1$ , $A_1=0.0015$ , $a=\left(0.0001,0,0\right)$ and for different values of $A_2=0.0015\left(\text{gray},\text{red}\right)$ , $0.15\left(\text{gray},\text{green}\right)$ , $0.35\left(\text{gray},\text{magenta}\right)$ , $0.55\left(\text{gray},\text{orange}\right)$ , panel-(c) for $\mu =0.1$ , $A_2=0.0015$ , $a=\left(0.0001,0,0\right)$ and for different values of $A_1=0.0015\left(\text{gray},\text{red}\right)$ , $0.15\left(\text{gray},\text{green}\right)$ , $0.35\left(\text{gray},\text{magenta}\right)$ , $0.55\left(\text{gray},\text{orange}\right)$ , panel-(d) shows the zoomed part of panel-(c) near the primary m₂.

From Figure 2(a), we have observed that when $a=\left(a_x,0,0\right)$ is increasing, the movement of AEPs L₁, L₂ and L₃ is almost negligible and the AEPs L₄ and L₅ move towards the y-axis. From Figure 2(b), we have observed that when A₂ is increasing, the AEP L₁ is shifted from right to left towards the bigger primary m₁,

the AEP L₂ is shifted from left to right away from the primary m₂, the AEP L₃ is shifted from left to right towards the bigger primary m₁, and the AEPs L₄ and L₅ move towards the x-axis.

From Figure 2, panel-c, we have observed that when A₁ is increasing, the AEP L₁ is shifted from left to right towards the primary m₂, the AEP L₂ is shifted from right to left towards the primary m₂, the AEP L₃ has almost negligible movement, and the AEPs L₄ and L₅ move towards the x-axis. In addition, we have calculated the numerical values of the AEPs and shown in Tables 1-3. We have observed that there exist three collinear and two non-collinear AEPs. Further, we have observed that the AEPs L₄ and L₅ are symmetric about the x-axis. Also, it is observed that the AEPs are the new positions of equilibrium points with the effect of continuous low-thrust and oblateness parameters which are different from the natural equilibrium points.

Table 1. The AEPs in the xy-plane when $a$ is varying.

Table 2. The AEPs in the xy-plane when A₂ is varying.

Table 3. The AEPs in the xy-plane when A₁ is varying.

4. Stability of the Artificial Equilibrium Points

To determine the linear stability of the system of AEPs in the low-thrust R3BP when both the primaries are oblate spheroid. We have followed the linear stability procedure of Morimoto et al. [16] . Firstly, we have linearized the equations of motion of the spacecraft and then linear stability is studied. To establish the spacecraft at a non-equilibrium point, a continuous low-thrust is provided to the spacecraft. Now, giving the small displacement to $\left(x_0\mathrm{,}{y}_0\mathrm{,}{z}_0\right)$ as $x=x_0+{\delta }_x,y=y_0+{\delta }_y,z=z_0+{\delta }_z,\left({\delta }_x,{\delta }_y,{\delta }_z\ll 1\right)$ . After using above displacements, the linearized equations corresponding to Equations (2) are given by

$\begin{array}{l}{\ddot{\delta }}_x-2n{\stackrel{\dot{}}{\delta }}_y={\Omega }_{xx}^0{\delta }_x+{\Omega }_{xy}^0{\delta }_y+{\Omega }_{xz}^0{\delta }_z,\\ {\ddot{\delta }}_y+2n{\stackrel{\dot{}}{\delta }}_x={\Omega }_{yx}^0{\delta }_x+{\Omega }_{yy}^0{\delta }_y+{\Omega }_{yz}^0{\delta }_z,\\ {\ddot{\delta }}_z={\Omega }_{zx}^0{\delta }_x+{\Omega }_{zy}^0{\delta }_y+{\Omega }_{zz}^0{\delta }_z,\end{array}\}$ (4)

where the superscript “0” in Equations (4) indicates that the values are to be calculated at the AEP $\left(x_0\mathrm{,}{y}_0\mathrm{,}{z}_0\right)$ under consideration. The characteristic root $\lambda$ satisfies the given characteristic equation

$\begin{array}{c}f\left(\lambda \right)={\lambda }^6+\left({\Omega }_{xx}^0+{\Omega }_{yy}^0+{\Omega }_{zz}^0+4n^2\right){\lambda }^4+({\Omega }_{xx}^0{\Omega }_{yy}^0+{\Omega }_{xx}^0{\Omega }_{zz}^0+{\Omega }_{yy}^0{\Omega }_{zz}^0\\ -{\left({\Omega }_{xy}^0\right)}^2-{\left({\Omega }_{xz}^0\right)}^2-{\left({\Omega }_{yz}^0\right)}^2+4n^2{\Omega }_{zz}^0){\lambda }^2+{\Omega }_{xx}^0{\Omega }_{yy}^0{\Omega }_{zz}^0\\ +2{\Omega }_{xy}^0{\Omega }_{xz}^0{\Omega }_{yz}^0-{\left({\Omega }_{xy}^0\right)}^2{\Omega }_{zz}^0-{\left({\Omega }_{xz}^0\right)}^2{\Omega }_{yy}^0-{\left({\Omega }_{yz}^0\right)}^2{\Omega }_{xx}^0\\ =0.\end{array}$ (5)

If a characteristic root $\lambda$ satisfies the Equation (5), then Equation (5) can be rewritten as

$\begin{array}{l}{\lambda }^6+\left({\Omega }_{xx}^0+{\Omega }_{yy}^0+{\Omega }_{zz}^0+4n^2\right){\lambda }^4+({\Omega }_{xx}^0{\Omega }_{yy}^0+{\Omega }_{xx}^0{\Omega }_{zz}^0+{\Omega }_{yy}^0{\Omega }_{zz}^0\\ -{\left({\Omega }_{xy}^0\right)}^2-{\left({\Omega }_{xz}^0\right)}^2-{\left({\Omega }_{yz}^0\right)}^2+4n^2{\Omega }_{zz}^0){\lambda }^2+{\Omega }_{xx}^0{\Omega }_{yy}^0{\Omega }_{zz}^0\\ +2{\Omega }_{xy}^0{\Omega }_{xz}^0{\Omega }_{yz}^0-{\left({\Omega }_{xy}^0\right)}^2{\Omega }_{zz}^0-{\left({\Omega }_{xz}^0\right)}^2{\Omega }_{yy}^0-{\left({\Omega }_{yz}^0\right)}^2{\Omega }_{xx}^0=0.\end{array}$ (6)

We see that all the powers of $\lambda$ in Equation (6) are even numbers and Equation (6) be a six degree equation in $\lambda$ . If $k={\lambda }^2$ , then we get

$\begin{array}{l}{k}^3+\left({\Omega }_{xx}^0+{\Omega }_{yy}^0+{\Omega }_{zz}^0+4n^2\right)k^2+({\Omega }_{xx}^0{\Omega }_{yy}^0+{\Omega }_{xx}^0{\Omega }_{zz}^0+{\Omega }_{yy}^0{\Omega }_{zz}^0\\ -{\left({\Omega }_{xy}^0\right)}^2-{\left({\Omega }_{xz}^0\right)}^2-{\left({\Omega }_{yz}^0\right)}^2+4n^2{\Omega }_{zz}^0)k+{\Omega }_{xx}^0{\Omega }_{yy}^0{\Omega }_{zz}^0\\ +2{\Omega }_{xy}^0{\Omega }_{xz}^0{\Omega }_{yz}^0-{\left({\Omega }_{xy}^0\right)}^2{\Omega }_{zz}^0-{\left({\Omega }_{xz}^0\right)}^2{\Omega }_{yy}^0-{\left({\Omega }_{yz}^0\right)}^2{\Omega }_{xx}^0=0.\end{array}$ (7)

Equation (7) is a cubic equation in k and can be rewritten as

$k^3+d_1{k}^2+d_{2}k+d_3=0,$ (8)

where

$d_1={\Omega }_{xx}^0+{\Omega }_{yy}^0+{\Omega }_{zz}^0+4n^2,$

$d_2={\Omega }_{xx}^0{\Omega }_{yy}^0+{\Omega }_{xx}^0{\Omega }_{zz}^0+{\Omega }_{yy}^0{\Omega }_{zz}^0-{\left({\Omega }_{xy}^0\right)}^2-{\left({\Omega }_{xz}^0\right)}^2-{\left({\Omega }_{yz}^0\right)}^2+4n^2{\Omega }_{zz}^0,$

$d_3={\Omega }_{xx}^0{\Omega }_{yy}^0{\Omega }_{zz}^0+2{\Omega }_{xy}^0{\Omega }_{xz}^0{\Omega }_{yz}^0-{\left({\Omega }_{xy}^0\right)}^2{\Omega }_{zz}^0-{\left({\Omega }_{xz}^0\right)}^2{\Omega }_{yy}^0-{\left({\Omega }_{yz}^0\right)}^2{\Omega }_{xx}^0\mathrm{,}$

and d₁, d₂, and d₃ are the real coefficients of k that depend on the second ordered derivatives of $\Omega$ with respect to x and y. Now, we determine the linear stability of the AEPs by finding the characteristic roots of Equation (8). We know that all the characteristic roots of a cubic equation are either real numbers or one of them is a real number and other characteristic roots are imaginary numbers. According to stability theory, a necessary and sufficient condition for an AEP to be linearly stable is that all the characteristic roots of Equation (5) lie in the left-hand side of the λ-plane (i.e., $\lambda \le 0$ ). If one or more characteristic roots of Equation (5) lie in the right-hand side of the λ-plane, then the system of AEPs is always unstable. If all the characteristic roots of Equation (5) lie to the left-hand side of λ-plane, then Equation (8) must have three real and negative roots. The resulting linear stability conditions according to Morimoto et al. [16] and Descartes sign rule, the system of AEPs is linearly stable if and only if $D\ge 0,d_1>0,d_2>0$ and $d_3>0$ , where D is the discriminant of the cubic Equation (8) and is given by:

$D=\frac{1}{4}{\left(d_3+\frac{2d_1^3-9d_1{d}_2}{27}\right)}^2+\frac{1}{27}{\left(d_2-\frac{d_1^2}{3}\right)}^3.$ (9)

It is concluded that the system of AEPs is linearly stable when $D\ge 0,d_1>0,$ $d_2>0$ and $d_3>0$ . Now, we have found the stability regions in the xy, xz and yz-planes as shown in Figures 3-8. In Figure 3, Figure 5, Figure 7, we have drawn the stability regions for the fixed values of $\mu =0.1$ , $A_1=0.0015$ and for different values of oblateness parameter $A_2=0.0015,0.15,0.35,0.55,0.75,0.95$ . In Figure 4, we have plotted the stability regions for the fixed values of $\mu =0.1$ , $A_2=0.0015$ and for different values of oblateness parameter $A_1=\mathrm{0.0015,0.015,0.035,0.055,0.075,0.095}$ . In Figure 6 and Figure 8, we have plotted the stability regions for the fixed values of $\mu =0.1$ , $A_2=0.0015$ and for different values of oblateness parameter $A_1=0.0015,0.15,0.35,0.55,0.75,0.95$ . From, Figures 3-8, we have observed that the stability regions decrease around both primaries for the increasing values of oblateness parameters $A_1\mathrm{,}{A}_2\in \left(\mathrm{0,1}\right)$ and for fixed value of mass parameter $\mu =0.1$ . Also, it is observed that the AEPs located in the stable regions are linearly stable otherwise unstable.

5. Zero Velocity Curves

In this section, we shall determine the possible regions of motion of the spacecraft in the low-thrust restricted thee-body problem when both the primaries are oblateness spheroid. The Jacobian Integral of the equations of motion (2) is defined as

$C=2\Omega +\left({\stackrel{\dot{}}{x}}^2+{\stackrel{\dot{}}{y}}^2+{\stackrel{\dot{}}{z}}^2\right).$ (10)

The Jacobian Integral of the equations of motion (2) with continuous low-thrust is defined as

Figure 3. Stable regions (gray area) in the xy-plane for fixed values of $\mu =0.1$ , $A_1=0.0015$ and for different values of oblateness parameter $A_2\left(0<A_2<1\right)$ (a) for $A_2=0.0015$ ; (b) $A_2=0.15$ ; (c) $A_2=0.35$ ; (d) $A_2=0.55$ ; (e) $A_2=0.75$ ; (f) $A_2=0.95$ .

Figure 4. Stable regions(gray area) in the xy-plane for $\mu =0.1$ , $A_2=0.0015$ and for different values of oblateness parameter $A_1\left(0<A_1<1\right)$ (a) for $A_1=0.0015$ ; (b) $A_1=0.015$ ; (c) $A_1=0.035$ ; (d) $A_1=0.055$ ; (e) $A_1=0.075$ ; (f) $A_1=0.095$ .

Figure 5. Stable regions (gray area) in the xz-plane for $\mu =0.1$ , $A_1=0.0015$ and for different values of oblateness parameter $A_2\left(0<A_2<1\right)$ (a) for $A_2=0.0015$ ; (b) $A_2=0.15$ ; (c) $A_2=0.35$ ; (d) $A_2=0.55$ ; (e) $A_2=0.75$ ; (f) $A_2=0.95$ .

Figure 6. Stable regions (gray area) in the xz-plane for $\mu =0.1$ , $A_2=0.0015$ and for different values of oblateness parameter $A_1\left(0<A_1<1\right)$ (a) for $A_1=0.0015$ ; (b) $A_1=0.15$ ; (c) $A_1=0.35$ ; (d) $A_1=0.55$ ; (e) $A_1=0.75$ ; (f) $A_1=0.95$ .

Figure 7. Stable regions (gray area) in the yz-plane for $\mu =0.1$ , $A_1=0.0015$ and for different values of oblateness parameter $A_2\left(0<A_2<1\right)$ (a) for $A_2=0.0015$ ; (b) $A_2=0.15$ ; (c) $A_2=0.35$ ; (d) $A_2=0.55$ ; (e) $A_2=0.75$ ; (f) $A_2=0.95$ .

Figure 8. Stable regions (gray area) in the yz-plane for $\mu =0.1$ , $A_2=0.0015$ and for different values of oblateness parameter $A_1\left(0<A_1<1\right)$ (a) for $A_1=0.0015$ ; (b) $A_1=0.15$ ; (c) $A_1=0.35$ ; (d) $A_1=0.55$ ; (e) $A_1=0.75$ ; (f) $A_1=0.95$ .

$C^{\prime }=2{\Omega }^{*}+\left({\stackrel{\dot{}}{x}}^2+{\stackrel{\dot{}}{y}}^2+{\stackrel{\dot{}}{z}}^2\right).$ (11)

The zero velocity curves have been determined from Equation (11) by taking $\stackrel{\dot{}}{x}=\stackrel{\dot{}}{y}=\stackrel{\dot{}}{z}=0$ . The black dots show the positions of the five AEPs, while the blue dots indicate the positions of two primaries m₁ and m₂. In Figures 9(a)-(d), we have plotted the ZVCs for fixed values of mass $\mu =0.1$ at the energy value of

Figure 9. The ZVCs in the low-thrust restricted three-body problem when both the primaries are oblate spheroid for fixed value of mass parameter $\mu =0.1$ (a) for fixed values of $C^{\prime }=-3.608652$ , $A_2=0.0015$ , $a=\left(0.0001,0,0\right)$ and for different values of $A_1=0.0015,0.049,0.095,0.187,0.25,0.3$ at the energy values of L₁; (b) for fixed values of $C^{\prime }=-3.608652$ , $A_1=0.0015$ , $a=\left(0.0001,0,0\right)$ and for different values of $A_2=0.0015,0.025,0.15,0.35,0.45,0.55$ ; Panel-(c) for fixed values of $A_1=0.0015$ , $A_2=0.0015$ , $a=\left(0.0001,0,0\right)$ and for different values of Jacobian constant $C^{\prime }=-3.608652,-3.478652,-3.288652,-3.108652,$ $-3.058652,-2.958652$ , and (d) for fixed values of $C^{\prime }=-3.608652$ , $A_1=0.0015$ , $A_2=0.0015$ , and for different values of low-thrust acceleration $a=\left(0.0001,0,0\right)$ , $\left(\mathrm{0.065,0,0}\right)$ , $\left(\mathrm{0.2,0,0}\right)$ , $\left(\mathrm{0.25,0,0}\right)$ , $\left(\mathrm{0.3,0,0}\right)$ , $\left(\mathrm{0.33,0,0}\right)$ .

L₁. The bounded curves in the panels-(a, b, c, d) indicate the forbidden regions. The forbidden regions are those regions where the motion of the spacecraft is not possible. The motion of the spacecraft is possible outside the bounded curves. We have observed that the spacecraft is free to move only in the regions outside the bounded curves. From Figure 9(a), we have observed that when A₁ is increasing the regions of motion increase in which the spacecraft can freely move. From Figure 9(b), it is observed that the regions of motion increase for the increasing values of oblateness parameter A₂ in which the spacecraft can move. On the other hand, from Figure 9(c), we have observed that when Jacobian constant $C^{\prime }$ is increasing the regions of motion increase in which the spacecraft can freely move. Further, from Figure 9(d), we have observed that when $a$ is increasing, the possible regions of motion increase in which the spacecraft can freely move. Furthermore, from Figures 9(a)-(d), we observe that the spacecraft can freely move from one primary to other for the increasing values of $A_1\mathrm{,}{A}_2\mathrm{,}{C}^{\prime }$ and $a$ respectively. Thus, the nature of the ZVCs in the low-thrust R3BP depend on the Jacobian constant $C^{\prime }$ , oblateness parameters $A_1\mathrm{,}{A}_2$ and continuous control acceleration $a$ of the low-thrust propulsion system of the spacecraft.

6. Conclusions

In this paper, we have studied the combined effect of oblateness of the primaries on the motion of the spacecraft in the low-thrust R3BP. The AEPs are obtained by introducing the continuous control acceleration at the non-equilibrium points. The numerical values of few AEPs have been calculated and displayed in Tables 1-3. It has been observed that there exist three collinear and two non-collinear AEPs for given parameters. We have observed that the non-collinear AEPs L₄ and L₅ are symmetric with respect to x-axis. The movements of AEPs have been studied graphically and shown in Figure 2. We find that the oblatness parameter of the bigger primary has less impact on the position of L₃ than oblateness of the smaller primary. Also, we have observed that the oblateness parameter of the primaries has more impact on the locations of the AEPs.

Further, we have plotted the stability regions in the xy, xz and yz-planes as shown in Figures 3-8. From, these figures, we have observed that the stability regions reduce around both the primaries m₁ and m₂ for the increasing values of oblateness parameters $A_1,A_2\in \left(0,1\right)$ and for fixed value of mass parameter $\mu =0.1$ . Also, we find that the oblateness of the primaries has more impact on the stable regions. Our results are different from Morimoto et al. [16] in some aspects like, 1) they have generated the AEPs in the low-thrust R3BP, whereas we have generated the AEPs in the low-thrust R3BP with the effect of oblateness of the primaries. In our case, the AEPs are new positions of natural equilibrium points different from McInnes et al. [14] , Morimoto et al. [16] , Baig and McInnes [17] , and Bu et al. [24] due to the presence of oblateness parameters $A_1\left(0<A_1<1\right)$ and $A_2\left(0<A_2<1\right)$ . When both the oblateness parameters A₁ and A₂ are zero and $a\ne \left(0,0,0\right)$ , the results obtained in this work are similar with the work of McInnes et al. [14] , Morimoto et al. [16] , Baig and McInnes [17] , and Bu et al. [24] . When $A_1=0$ , $A_2=0$ and $a=\left(0,0,0\right)$ , the obtained results are similar with the work of Szebehely [1] . 2) they have obtained the stable regions in the Sun-Earth system, whereas we have obtained the stable regions for $\mu =0.1$ and for different values of oblateness parameters $A_1\left(0<A_1<1\right)$ and $A_2\left(0<A_2<1\right)$ .

Finally, we have determined the ZVCs to study the possible regions of motion in which the spacecraft is free to move. We have observed that the regions of motion increase in which the spacecraft can freely move from one place to other place. Further, it has been observed that the unreachable regions can become reachable in the presence of continuous low-thrust. This paper is applicable in the Earth-Moon system for communications for the spacecraft missions.

Conflicts of Interest

The authors declare no conflicts of interest regarding the publication of this paper.

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