## General Integral for a Class of NonSteady Atmospheric Flights and Applications to Trajectory Analysis

**Authors:**Azimov DM^{1}, Mukharlyamov RG^{2}**Affiliations:**- The University of Hawaii at Manoa
- Peoples’ Friendship University of Russia (RUDN University)

**Issue:**Vol 25, No 2 (2017)**Pages:**161-169**Section:**Theoretical Mechanics**URL:**http://journals.rudn.ru/miph/article/view/15803**DOI:**https://doi.org/10.22363/2312-9735-2017-25-2-161-169- Cite item

# Abstract

A complete analytical integration of the aircraft kinematic and dynamic equations of motion is presented. Different applications of defined integrals to trajectory analysis are considered. The dynamic equations are obtained under the assumptions, that acceleration due to aerodynamic lift, the difference between the accelerations due to propulsive thrust and aerodynamic drag are not changed, the aircraft body rate about the velocity axis is zero and the sideslip angle is zero. The general integral of these equations consists of six independent first integrals of motion and describes a class of non-steady flight trajectories in a maneuver plane. It will be shown that the dynamic equations can be derived and completely integrated in a closed-form for more general assumptions. The problem of computing thrust for a given trajectory has been considered. The trajectory is defined by constraint equation. Constraints stabilization equations, which have asymptotically stable trivial solution, are constructed. Explicitness can make the integrals applicable to modeling the trajectories of spacecraft, re-entry vehicles and missiles, and to the design of on-board targeting and guidance. An illustrative example is presented.

# Full Text

1. Introduction This paper presents a complete analytical integration of the aircraft kinematic and dynamic equations obtained under the following assumptions: (a) acceleration due to aerodynamic lift, and the difference between the accelerations due to propulsive thrust and aerodynamic drag are not changed; (b) the aircraft body rate about the velocity axis is zero; (c) the sideslip angle is zero. It will be shown that the general integral of these equations consists of six independent first integrals which lead to the closed-form analytical solutions. The studies of the existing literature show that the aircraft equations can be integrated in a closed-form for some specific cases of quasi-steady and non-steady flights, including the cases of climb and cruise with constant altitude, velocity or lift acceleration, negligible flight path angle or small angle of attack [1, 2]. In some cases of optimal quasi-steady cruise trajectories, the equations of motion have been implicitly integrated or reduced to quadratures [2]. It should be noted that the studies presented in this paper were initiated with the purpose of integration of the 3rd order differential equation, obtained for the nonlinear model of the aircraft tracking problem under the following assumptions: (1) acceleration due to aerodynamic lift, and the difference between the accelerations due to propulsive thrust and aerodynamic drag are not changed; (2) the aircraft body rate about the roll axis is zero; (3) the angle of attack and the sideslip angle are zero [3-5]. Note that the left hand side of Eq. (1) represents the jerk vector, and its expression does not explicitly depend on the accelerations due to thrust, drag and lift. Analysis show, however, that as the drag is a function of the square of the velocity, it would be very difficult to hold the lift, and the thrust-drag accelerations constant with zero angle of attack. In this paper, it will be shown that Eq. (1) can also be derived and completely integrated in a closed-form for a more general assumptions (a-c) with non-zero and variable angles of attack. It is demonstrated that the assumptions (a-b) can significantly extend the applicability of Eq. (1). Explicitness can make the integrals applicable to modeling the trajectories of spacecraft, re-entry vehicles and missiles, and to the design of on-board targeting and guidance [4]. 2. Equations and Integrals for Non-steady Flight Consider the F-frame formed by the triad of orthogonal unit vectors e�� , e , e and with the origin at the aircraft center of mass (COM): the unit vector e is aligned with the velocity vector, e forms the angle with lift and e completes the right handed system (see Fig. 1). The angle is measured in the e e -plane. It is assumed that the non-steady flight trajectory lies in a vertical plane containing e and e�� . Then if P is the sum of external forces acting on the aircraft, that is thrust, weight, drag and lift, then [1] Figure 1. To the nonlinear aircraft model can be rewritten in the form: P = ( cos ¯ - - 0 sin )e + [( sin ¯ + ) cos - 0 cos ]e , where ¯ = + is the angle between the thrust vector and the velocity vector. If a = ˙ e + ˙ e�� , then with the assumptions given above, the Newton’s second law yields the following equations valid in the maneuver -plane [3]: (2) where (3) with = const. Complete analytical integration of Eqs. (2) and application of the resulting solutions to trajectory analysis is the main purpose of this paper. As will be shown below, the complete integration of Eqs. (2) reveals a general integral which consists of six independent first integrals with their constants. These constants will be denoted below by , ( = 1, . . . , 6), and one can accept that 1 = 1 = const and 2 = 2 = const. Eqs. (2) are valid for a flight with the assumptions (a-c) in the maneuver plane. The first integrals of Eqs. (2) for 1 and 2 represent the relationships between the velocity magnitude, flight path angle, the propulsive and aerodynamic accelerations. 3. Integrals for Velocity Vector, Time and Position Vector Integrals for magnitude of velocity vector In this subsection, it will be shown that the first two equations of Eqs. (2) can be explicitly integrated in elementary and transcendental functions in terms of the angle . By considering as an independent variable instead of time, , we have ˙ d/d d/d. Then by eliminating d/d from Eqs. (2), one can obtain which can be integrated in the form [6]: (5) where 3 is the integration constant, = + , ¯ = /2 and + sin ̸= 0, and thefollowing constants are used: (7) Note that in a particular case when + sin = 0, the system of equations in Eqs. (2) describes a motion with constant and . This case is of a very limited theoretical and practical interest, and not considered in this paper. Integrals for time Once = ��() is determined, the second equation of Eqs. (2) can be integrated as: which can be reduced to the following final forms: where 4 is the new integration constant, sin = 1. As Eq. (1) is a 3rd-order vector differential equation, which describes the motion in the maneuver plane, its complete integration would require to find six independent first integrals with six scalar integration constants of motion in the maneuver plane. So far, four independent first integrals and four new constants have been found above, that is 1 and 2 in Eq. (2), 3 in Eqs. (5) and 4 in Eqs. (9). Eqs. (5) and Eqs. (9) also represent the general solution of Eqs. (2) with constants 3, 4, 1 and 2. Integrals for position vector components It can be shown that the magnitude of the velocity vector and angle between the velocity vector and the local horizon are not enough to uniquely determine the position of the aircraft in the maneuver plane. If v = cos i sin i and r = i i�� , where and are the aircraft horizontal and vertical coordinates (crossrange and downrange respectively), then the equation v = r˙ written in terms of its components yields (10) Noting that = /2, ˙ = d/d d/d and ˙ Eqs. (10) as = d/d d/d, one can rewrite Integration of Eqs. (11) yields the aircraft coordinates and : (12) and (13) where 5 and 6 are the new integration constants, ¯ = /2, and and are known functions of . Eqs. (12) and (13) represent the first integrals of Eqs. (10) (and Eqs. (2)), and allow us to determine the aircraft’s horizontal and vertical cartesian coordinates (crossrange and downrange) in the maneuver plane. The first integrals presented in Eqs. (2), (5), (9), (12) and (13) with constants , = 1, . . . , 6 represent the general integral of Eq. (2). Any point on the trajectory can be considered as a target point and the constants can be chosen to achieve this point. Consequently, the targeting problem can be solved at any desired point thereby providing a foundation for the development and design of the targeting and guidance schemes. 4. Expressions for Thrust and Angle of Attack As mentioned above, the assumptions (a)-(c) can be justified and validated by analyzing the thrust, drag and list accelerations using the solutions for altitude and velocity, and by comparing the results for the angle of attack and the thrust to existing ranges of these quantities [2, 7, 8]. The assumptions (a) and (b) mean that where [1] and it is assumed that = /2 + , = 0, 1, 2 . . . , the drag and lift coefficients, and can be computed according to Ref. [2] and the air density, is changed according to the exponential law. From Eq. (14) one can obtain Eq. (15) is a transcendental equation and solvable for = ��(, ) only by numerical schemes. Once = ��(, ) is determined, then the thrust can be computed as (16) 5. Illustrative Example Consider the example of a flight simulation using the analytical solutions presented above for 2 > 2. One can compute magnitude of velocity vector, time, altitude and downrange in terms of the angle which is assumed to satisfy the inequality: 0 1. The following values have been accepted: 0 = 0.0, 0 = 250, 0 = 9.8, = 9.8, 0 = 28500, 0 = 7000, = 5000, = 10.0, [0.1, 0.5], 0 = 10∘, ∆ = 65∘. The results of the simulations for this case are illustrated in figures 2-4. The plots of the angle of attack and the thrust vs magnitude of velocity are presented in figures 2 and 3. These figures show that when the velocity magnitude is decreased in the beginning of the simulation for 10 ft/s, is increased for 0.5∘ and is decreased for 45 lbs. Analysis has also shown that an increase in values of leads to the higher values for and �� , and also is increased together with altitude and Mach number, computed as = /, where is the speed of sound [2]. From Fig. 4 it can also be seen that each additional value 0.1 to would yield an increase of the final altitude by only 100 m. Figure 2. Angle of attack vs magnitude of velocity Figure 3. Propulsive thrust vs magnitude of velocity Figure 4. Downrange vs altitude 6. Computation of Thrust with Stabilization of Constraints Let the aircraft trajectory be given in the form = (). Then the equations of a programmed constraint and its derivative are = - () and d = with [9] (17) The equations of the perturbed constraint can be given as (18) d and in particular, respect to the thrust: = - - . Eqs. (2), (17) and (18) yield the equation with After substitution of these expressions into Eqs. (18), which provides one can obtain the equation for determination of �� : = /, where Assume now that = = () + sin + ′() cos , with > 0, > 0. Then one can show that 7. Conclusions The general integral of the aircraft’s kinematic and dynamic equations of motion in the non-steady flight conditions has been obtained. These equations represent the 3rd order vector differential equation, the general integral of which consists of six independent first integrals with six corresponding constants. All integrals are expressed in elementary and transcendental functions in terms of the flight path angle. The applications may also include the flight trajectories in the transonic, low and high supersonic conditions. These results can find potential applications in the design of on-board targeting and guidance schemes.# About the authors

### D M Azimov

The University of Hawaii at Manoa
Email: azimov@hawaii.edu

2540 Dole St., Holmes 202A, Honolulu, HI, 96822, USA

Department of Mechanical Engineering

### R G Mukharlyamov

Peoples’ Friendship University of Russia (RUDN University)
Email: robgar@mail.ru

6 Miklukho-Maklaya St., Moscow, 117198, Russian Federation

Department of Theoretical Physics and Mechanics