Hoisting container pose control method of double-rope winding type ultra-deep vertical shaft hoisting system

Abstract

The present invention discloses a hoisting container pose control method of a double-rope winding type ultra-deep vertical shaft hoisting system. The method comprises the following steps of step 1, building a mathematical model of a double-rope winding type ultra-deep vertical shaft hoisting subsystem; step 2, building a position closed-loop mathematical model of an electrohydraulic servo subsystem; step 3, outputting a flatness characteristics of a nonlinear system; step 4, designing a pose leveling flatness controller of a double-rope winding type ultra-deep vertical shaft hoisting subsystem; and step 5, designing a position closed-loop flatness controller of the electrohydraulic servo subsystem.

Description

CROSS-REFERENCE TO RELATED APPLICATION

This application is a 371 of international application of PCT application serial no. PCT/CN2019/105589, filed on Sep. 12, 2019, which claims the priority benefit of China application no. 201910284619.2, filed on Apr. 10, 2019. The entirety of each of the above mentioned patent applications is hereby incorporated by reference herein and made a part of this specification.

FIELD OF THE INVENTION

The present invention relates to a vertical shaft hoisting system, in particular to a hoisting container pose control method of a double-rope winding type ultra-deep vertical shaft hoisting system, and belongs to the technical field of mine hoisting.

DESCRIPTION OF RELATED ART

An ultra-deep vertical shaft hoisting system is a vertical shaft hoisting system with a mining depth greater than 1500 m. Due to the great mining depth of the ultra-deep vertical shaft hoisting system, a common rigid hoisting container cage guide is prone to generate damage phenomena such as deformation of a cage guide in a shaft, damage to a cage guide beam, looseness of a beam socket and operation instability under conditions of high-speed and heavy-load operation of a hoisting container, so that the common rigid hoisting container cage guide cannot be used for ultra-deep vertical shaft hoisting. However, when a flexible cage guide is used for hoisting, factors of manufacturing differences of diameters of winding drums, installation differences of two steel wire ropes, elastic modulus inconsistency of the two steel wire ropes, etc. may cause asynchronism of tail end movement of the two steel wire ropes of the hoisting system, so that inclination of the hoisting container is caused, and tension inconsistency of the two steel wire ropes is further caused. When the steel wire ropes operate under such conditions for a long time, a condition that the stress of one steel wire rope exceeds its safe use stress is easily caused, so that major malignant accidents of rope fracture is caused. In order to avoid such accidents, an angle of the hoisting container needs to be actively regulated, so that the hoisting container keeps a balanced state, and the tension of the two steel wire ropes keeps consistent.

A backstepping controller design method is commonly used in the prior art, but such a control method needs to perform variable derivation on system state variables, and a design process of a controller is complicated. Additionally, when the controller is applied to a practical system of an ultra-deep vertical shaft, since the ultra-deep vertical shaft hoisting system is a complicated multi-structure mechanical-electrical-hydraulic system, even though many practical factors are considered in a modeling process, it is difficult to realize consistency with the practical system. Therefore, in the design process of the controller, the derivation on the system state variables will undoubtedly amplify sensor measurement noise and system non-modeling characteristics, and cause greater tracking errors and longer leveling response time.

SUMMARY OF THE INVENTION

In order to overcome various defects in the prior art, the present invention provides a hoisting container pose control method of a double-rope winding type ultra-deep vertical shaft hoisting system. A design process is simple. Control performance is good. Fast response may be given to a leveling hoisting system. Tracking errors are small.

In order to achieve the invention objectives, the present invention provides the hoisting container pose control method of the double-rope winding type ultra-deep vertical shaft hoisting system. The method includes following steps:

step 1, building a mathematical model of a double-rope winding type ultra-deep vertical shaft hoisting subsystem;

step 2, building a position closed-loop mathematical model of an electrohydraulic servo subsystem;

step 3, outputting flatness characteristics of a nonlinear system;

step 4, designing a flatness controller of a double-rope winding type ultra-deep vertical shaft hoisting subsystem; and

step 5, designing a position closed-loop flatness controller of the electrohydraulic servo subsystem.

Further, the mathematical model of the double-rope winding type ultra-deep vertical shaft hoisting subsystem in step 1 is as follows:

1) Parameters used in a modeling process are defined:

l_ri (i=1,2) is a winding length of a duplex winding drum;

l_ci (i=1,2) is a length of two string ropes in a process of hoisting or descending a hoisting container;

l_hi (i=1,2) is a length of two vertical section steel wire ropes in the process of hoisting or descending the hoisting container;

u_i(i=1,2) is displacement of two floating hoisting sheaves;

φ_i is an included angle between the two string ropes and a horizontal plane;

a_i(i=1,2) is a horizontal distance between a connecting point of the two vertical section steel wire ropes on the hoisting container and a gravity center of the hoisting container;

b_i(i=1,2) is a vertical distance between upper and lower surfaces of the hoisting container and the gravity center of the hoisting container;

k_si(i=1,2,3,4) is a transverse equivalent stiffness of four pairs of spring-damping models; and

c_si(i=1,2,3,4) is a transverse equivalent damping coefficient of the four pairs of spring-damping models.

2) A hoisting process is defined as a positive direction, and in the process of hoisting or descending the hoisting container, the lengths of the two vertical section steel wire ropes 5 are shown as follows:l_h1=l_h10−l_r1−u₁ sin(φ₁)  (1); andl_h2=l_h20−l_r2−u₂ sin(φ₂)  (2), wherein

l_h10 and l_h20 are initial lengths of the two vertical section steel wire ropes.

3) A hoisting subsystem generalized vector q=[x_c,y_c,θ] is defined, wherein x_c and y_c are respectively vertical displacement and horizontal displacement of the gravity center of the hoisting container 6, θ is an anticlockwise rotation angle of the hoisting container 6, and a Lagrange's dynamical equation of the hoisting subsystem is shown as follows:

$\begin{array}{cc}\frac{d}{\mathrm{dt}}\left(\frac{\partial T}{\partial \stackrel{.}{q}}\right)-\frac{\partial T}{\partial q}+\frac{\partial D}{\partial \stackrel{.}{q}}+\frac{\partial U}{\partial q}=Q,& \left(3\right)\end{array}$ wherein

T, U and D are respectively the kinetic energy, potential energy and Rayleigh's dissipation function of the hoisting system, and Q is a hoisting subsystem nonpotential generalized force not including damping.

4) Tangential point displacement between the floating hoisting sheave and the left string rope is l_r1+u₁(1+sin φ₁), and tangential point displacement between the floating hoisting sheave and the left vertical section steel wire rope is l_r1+u₁(1+sin φ₁).

Displacement of the left string rope in a position of s unit length distance is shown as follows:

$\begin{array}{cc}{s}_D=I_{r1}+\left(l_{r1}-{\mu }_1{\sin \varphi }_1-l_{r1}\right)\frac{s}{l_{r1}}.& \left(4\right)\end{array}$

Similarly, displacement of the left vertical section rope in a position of y unit length distance is shown as follows:

$\begin{array}{cc}{y}_{l1}=l_{r1}+\left(1+\sin {\phi }_1\right)u_1+\left[\left(x_c-a_1{\theta }_c\right)-l_{r1}-\left(1+\sin {\phi }_1\right)u_1\right]\frac{y}{l_{h1}}.& \left(5\right)\end{array}$

5) According to formulas (4) and (5), kinetic energy formulas of the left string rope and the left vertical section steel wire rope are respectively shown as follows:

$\begin{array}{cc}\begin{array}{c}{T}_{\mathrm{lc}1}=\frac{1}{2}\rho {{\int }_0}^{l_{c1}}{\stackrel{.}{s}}_{l1}^2\mathrm{ds}\\ =\frac{1}{2}\rho {{\int }_0}^{l_{c1}}{\left[{\stackrel{.}{l}}_{r1}+\left({\stackrel{.}{l}}_{r1}-{\stackrel{.}{u}}_1\sin {\phi }_1-{\stackrel{.}{l}}_{r1}\right)\frac{s}{l_{c1}}\right]}^2\mathrm{ds}\\ =\frac{1}{6}\rho l_{c1}\left[{\stackrel{.}{l}}_{r1}^2+{\stackrel{.}{l}}_{r1}\left({\stackrel{.}{l}}_{r1}-{\stackrel{.}{u}}_1\sin {\phi }_1\right)+{\left({\stackrel{.}{l}}_{r1}-{\stackrel{.}{u}}_1\sin {\phi }_1\right)}^2\right]\end{array},\mathrm{and}& \left(6\right)\end{array}$ $\begin{array}{cc}\begin{array}{c}{T}_{l_{h1}}=\frac{1}{2}\rho {{\int }_0}^{l_{h1}}{\stackrel{.}{y}}_{l1}^2\mathrm{dy}\\ =\frac{1}{2}\rho {{\int }_0}^{l_{h1}}\{{\stackrel{.}{l}}_{r1}+\left(1+\sin {\alpha }_1\right){\stackrel{.}{u}}_1+\\ {\left[\left({\stackrel{.}{x}}_c-{\phi }_1{\stackrel{.}{\theta }}_c\right)-{\stackrel{.}{l}}_{r1}-\left(1+\sin {\phi }_1\right){\stackrel{.}{u}}_1\right]\frac{y}{l_{h1}}\}}^2\mathrm{dy}\\ =\frac{1}{6}\rho {l_{h1}\left[\{{\stackrel{.}{l}}_{r1}+(1+\sin {\phi }_1{\stackrel{.}{u}}_1\right]}^2+\left({\stackrel{.}{x}}_c-a_1{\stackrel{.}{\theta }}_c\right)\\ \left[{\stackrel{.}{l}}_{r1}+\left(1+\sin {\phi }_1\right){\stackrel{.}{u}}_1\right]+{\left({\stackrel{.}{x}}_c-a_1{\stackrel{.}{\theta }}_c\right)}^2\}\end{array},\mathrm{wherein}& \left(7\right)\end{array}$ wherein

in the formulas, ρ is unit mass of the steel wire rope.

6) Tangential point displacement between the floating hoisting sheave and the right string rope is l_r2−u₂ sin φ₂, and displacement of the right string rope in the position of the s unit length distance is shown as follows:

$\begin{array}{cc}{s}_{l2}=l_{r2}+\left(l_{r2}-u_2\sin {\phi }_2-l_{r2}\right)\frac{s}{l_{h1}}.& \left(8\right)\end{array}$

Tangential point displacement between the floating hoisting sheave and the right vertical section steel wire rope is l_r2+u₂(1+sin φ₂), and displacement of the right vertical section rope in the position of the y unit length distance is shown as follows:

$\begin{array}{cc}{y}_{t2}=l_{r2}+\left(1+\sin {\phi }_2\right)u_2+\left[\left(x_c-a_2{\theta }_c\right)-l_{r2}-\left(1+\sin {\phi }_2\right)u_2\right]\frac{y}{l_{h2}}.& \left(9\right)\end{array}$

7) According to formulas (8) and (9), kinetic energy formulas of the right string rope and the right vertical section steel wire rope are respectively shown as follows:

$\begin{array}{cc}\begin{array}{c}{T}_{l_{c2}}=\frac{1}{2}\rho {{\int }_0}^{l_{c2}}{\stackrel{.}{s}}_l^2\mathrm{ds}\\ =\frac{1}{2}\rho {{\int }_0}^{l_{c2}}{\left[{\stackrel{.}{l}}_{r2}+\left({\stackrel{.}{l}}_{r2}-{\stackrel{.}{u}}_2\sin {\phi }_2-{\stackrel{.}{l}}_{r2}\right)\frac{s}{l_{c2}}\right]}^2\mathrm{ds}\\ =\frac{1}{6}\rho l_{c2}\left[{\stackrel{.}{l}}_{r2}^2+{\stackrel{.}{l}}_{r2}\left({\stackrel{.}{l}}_{r2}-{\stackrel{.}{u}}_2\sin {\phi }_2\right)+{\left({\stackrel{.}{l}}_{r2}-{\stackrel{.}{u}}_2\sin {\phi }_2\right)}^2\right]\end{array},\mathrm{and}& \left(10\right)\end{array}$ $\begin{array}{cc}\begin{array}{c}{T}_{l_{h2}}=\frac{1}{2}\rho {{\int }_0}^{l_{h2}}{\stackrel{.}{y}}^{2_l}\mathrm{dy}\\ =\frac{1}{2}\rho {{\int }_0}^{l_{h2}}\{{\stackrel{.}{l}}_{r2}+\left(1+\sin {\phi }_2\right){\stackrel{.}{u}}_2+\\ {\left[\left({\stackrel{.}{x}}_c+a_2{\stackrel{.}{\theta }}_c\right)-{\stackrel{.}{l}}_{r2}-\left(1+\sin {\phi }_2\right){\stackrel{.}{u}}_2\right]\frac{y}{l_{h2}}\}}^2\mathrm{dy}\\ =\frac{1}{6}\rho {l_{h2}\left[\{\stackrel{.}{l}+\left(1+\sin {\phi }_2\right){\stackrel{.}{u}}_2\right]}^2+\left({\stackrel{.}{x}}_c+a_2{\stackrel{.}{\theta }}_c\right)\\ \left[{\stackrel{.}{l}}_{r2}+\left(1+\sin {\phi }_2\right){\stackrel{.}{u}}_2\right]+{\left({\stackrel{.}{x}}_c-a_2{\stackrel{.}{\theta }}_c\right)}^2\}\end{array}.& \left(11\right)\end{array}$

8) Kinetic energy formulas of the left and right floating hoisting sheaves are shown as follows:

$\begin{array}{cc}{T}_{h1}=\frac{1}{2}{m}_1{\stackrel{.}{u}}_1^2+\frac{1}{2}{I_1\left(\frac{{\stackrel{.}{l}}_{r1}}{r_1}\right)}^2,\mathrm{and}& \left(12\right)\end{array}$ $\begin{array}{cc}{T}_{h2}=\frac{1}{2}{m}_2{\stackrel{.}{u}}_2^2+\frac{1}{2}{I_2\left(\frac{{\stackrel{.}{l}}_{r2}}{r_2}\right)}^2,& \left(13\right)\end{array}$

in the formulas, m₁ and m₂ are respectively masses of the left and right floating hoisting sheaves, r₁ and r₂ are respectively radii of the left and right floating hoisting sheaves, and I₁ and I₂ are respectively rotational inertias of the left and right floating hoisting sheaves.

A kinetic energy formula of the hoisting container is shown as follows:T_c=½m_c{dot over (x)}_c²+½m_c{dot over (y)}_c²+½I_c{dot over (θ)}_c²  (14), wherein

in the formula, m_c is a mass of the hoisting container, and I_c is a rotational inertia of the hoisting container.

9) A potential energy formula of the left steel wire rope is shown as follows:U_i1=½ρgl_h1[x_c−α₁θ_c)+l_r1+(1+sin φ₁)u₁]−½ρgl_c1(l_r1+u₁ sin φ₁+l_r1)sin φ₁+½k_c1(l_r1−u₁ sin φ₁−l_r1)²+½k_h1[(x_c−α₁θ_c)−l_r1−(1+sin φ₁)u₁]²  (15); and

a potential energy formula of the right steel wire rope is shown as follows:U_i2=½ρgl_h2[x_c−α₂θ_c)+l_r2+(1+sin φ₂)u₂]−½ρgl_c2(l_r2+u₂ sin φ₂+l_r2)sin φ₂+½k_c2(l_r2−u₂ sin φ₂−l_r2)²+½k_h2[(x_c−α₂θ_c)−l_r2−(1+sin φ₂)u₂]²  (16); wherein

in the formulas, k_c1 and k_h1 are respectively stiffness of the left string rope and the left vertical section steel wire rope, and k_c2 and k_h2 are respectively stiffness of the right string rope and the right vertical section steel wire rope.

Potential energy formulas of the left and right floating hoisting sheaves are respectively shown as follows:U_h1=m₁gu₁  (17), andU_h2−m₂gu₂  (18).

Potential energy of the hoisting container system includes the potential energy of the hoisting container and the potential energy of a flexible cage guide, and a formula is shown as follows:U_c=m_cgx_c+½k_s1(y_c−b₁θ_c)²+½k_s2(γ_c+b₂θ_c)²+½k_s3(γ_c−b₁θ_c)²+½k_s4(γ_c+b₂θ_c)²  (19).

10) Rayleigh's dissipation energy formulas of left and right ropes are respectively shown as follows:D_l1=½c_c1(i_r1−{dot over (u)}₁ sin φ₁−i_r1)²+½c_h1[{dot over (x)}_c−a₁{dot over (θ)}_c)−i_r1−(1+sin φ₁){dot over (u)}₁]²  (20); andD_l2=½c_c2({dot over (l)}_r2−{dot over (u)}₂ sin φ₂−i_r12)²+½c_h2[({dot over (x)}_c+a₂{dot over (θ)}_c)−{dot over (l)}_r2−(1+sin φ₂){dot over (u)}₂]²  (21), wherein

in the formulas, c_c1 and c_h1 are respectively damping coefficients of the left string rope and the left vertical section steel wire rope, and c_c2 and c_h2 are respectively damping coefficients of the right string rope and the right vertical section steel wire rope.

A Rayleigh's dissipation energy formula of the hoisting container system is shown as follows:D_c=½c_s1({dot over (y)}_c−b₁{dot over (θ)}_c)²+½c_s2({dot over (y)}_c+b₂{dot over (θ)}_c)²+½c_s3({dot over (y)}_c−b₁{dot over (θ)}_c)²+½c_s4({dot over (y)}_c+b₂{dot over (θ)}_c)²  (22).

Based on the above, the kinetic energy, the potential energy and the Rayleigh's dissipation energy of the hoisting subsystem are respectively shown as follows:T=T_l11+T_l12+T_l21+T_l22+T_h1+T_h2+T_c  (23),U=U_l1+U_l2+U_h1+U_h2+U_c  (24), andD=D_l1+D_l2+D_c  (25).

11) The above formulas are substituted into a general equation:M{umlaut over (q)}+C{dot over (q)}+Kq=F  (26), wherein

in the formula, {circumflex over (q)},{dot over (q)} and q are respectively a generalized acceleration, speed and displacement, and M, C, K and F are respectively a mass matrix, a damping matrix, a stiffness matrix and a non-potential force of the hoisting subsystem, so that following formulas are obtained:

$\begin{array}{cc}M=\left[\begin{array}{ccc}{m}_c+\frac{1}{3}\rho l_{h1}+\frac{1}{3}\rho l_{h2}& 0& -\frac{1}{3}\rho l_{k1}{a}_1+\frac{1}{3}\rho l_{h2}{a}_2\\ 0& m_c& 0\\ -\frac{1}{3}\rho l_{h1}{a}_1+\frac{1}{3}\rho l_{h2}{a}_2& 0& l_c-\frac{1}{3}\rho l_{h1}{a}_1^2+\frac{1}{3}\rho l_{h2}{a}_2^2\end{array}\right],& \left(1–2\right)\end{array}$ $\begin{array}{cc}C=\left[\begin{array}{ccc}{c}_{h1}+\frac{1}{3}\rho {\stackrel{.}{l}}_{h1}+c_{h2}\frac{1}{3}\rho {\stackrel{.}{l}}_{h2}& 0& -(a_2\\ 0& c_{s1}+c_{s2}+c_{s3}+c_{s4}& -c_{s1}{b}_1+c_{s2}{b}_2-c_{s3}{b}_1+c_{s4}{b}_1\\ \begin{array}{c}-\left(c_{h1}+\frac{1}{3}\rho {\stackrel{.}{l}}_{h1}\right)a_1+\\ \left(c_{h2}\frac{1}{3}\rho {\stackrel{.}{l}}_{h2}\right)a_2\end{array}& \begin{array}{c}-c_{s1}{b}_1+c_{s2}{b}_2-\\ c_{s3}{b}_1+c_{s4}{b}_1\end{array}& \begin{array}{c}\left(c_{h1}+\frac{1}{3}\rho {\stackrel{.}{l}}_{h1}\right)a_1^2+\left(c_{h2}+\frac{1}{3}\rho {\stackrel{.}{l}}_{h2}\right)a_2^2+\\ b_1^2{c}_{\mathrm{s1}}+b_2^2{c}_{s2}+b_1^2{c}_{s3}+b_2^2{c}_{s4}\end{array}\end{array}\right],& \left(1–3\right)\end{array}$ $\begin{array}{cc}\left[\begin{array}{ccc}{k}_{h1}+k_{h2}& 0& -k_{h1}{a}_1+k_{h2}{a}_2\\ 0& k_{s1}+k_{s2}+k_{s3}+k_{s4}& -k_{s1}{b}_1+k_{s2}{b}_2-k_{s3}{b}_1+k_{s4}{b}_2\\ -k_{h1}{a}_1+k_{h2}{a}_2& -k_{s1}{b}_1+k_{s2}{b}_2-k_{s3}{b}_1+k_{s4}{b}_2& k_{h1}{a}_1^2+k_{h2}{a}_2^2+b_1^2{k}_{s1}+b_2^2{k}_{s2}+b_1^2{k}_{s3}+b_2^2{k}_{s4}\end{array}\right],\mathrm{and}& \left(1–4\right)\end{array}$ $\begin{array}{cc}F=\left[\begin{array}{c}-\frac{1}{6}\rho l_{h1}\left[{\ddot{l}}_{r1}+({\ddot{u}}_1\left(1+\sin {\varphi }_1\right)\right]-\frac{1}{6}\rho l_{h2}\left[{\ddot{l}}_{r2}+({\ddot{u}}_2\left(1+\sin {\phi }_2\right)\right]+\\ \left(-\frac{1}{6}\rho {\stackrel{.}{l}}_{h1}+c_{h1}\right)\left[{\ddot{l}}_{r1}+{\stackrel{.}{u}}_1\left(1+\sin {\phi }_1\right)\right]+\left(-\frac{1}{6}\rho {\stackrel{.}{l}}_{h2}+c_{h2}\right)\left[{\stackrel{.}{l}}_{r2}+{\stackrel{.}{u}}_2\left(1+\sin {\phi }_2\right)\right]+k_{h1}\\ \left[l_{r1}+u_1\left(1+\sin {\phi }_1\right)\right]+k_{h2}\left[l_{h2}+n_2\left(1+\sin {\phi }_2\right)\right]-m_{c}g-\frac{1}{2}\rho l_{h1}-\frac{1}{2}\rho l_{h2}\\ 0\\ \frac{1}{6}\rho l_{h1}{a}_1\left[{\ddot{l}}_{r1}+{\ddot{u}}_1\left(1+\sin {\phi }_1\right)\right]-\frac{1}{6}\rho l_{h2}\left[{\ddot{l}}_{r2}+{\ddot{u}}_2\left(1+\sin {\phi }_2\right)\right]+\\ \left(-\frac{1}{6}\rho {\stackrel{.}{l}}_{h1}+c_{h1}\right)a_1\left[{\stackrel{.}{l}}_{r1}+{\stackrel{.}{u}}_1\left(1+\sin {\phi }_1\right)\right]-\left(-\frac{1}{6}\rho {\stackrel{.}{l}}_{h2}+c_{h2}\right)a_2\left[{\stackrel{.}{l}}_{r2}+{\stackrel{.}{u}}_2\left(1+\sin {\phi }_2\right)\right]+k_{h1}{a}_1\\ \left[l_{r1}+u_1\left(1+\sin {\phi }_2\right)\right]-k_{h2}{a_2\left[l_{r2}+u_2\left(1+\sin \phi \right)\right]}_2+\frac{1}{2}\rho {\mathrm{gl}}_{h1}{a}_1-\frac{1}{2}\rho {\mathrm{gl}}_{h2}{a}_2\end{array}\right].& \left(1–5\right)\end{array}$

12) A system equation is simplified. In the modeling process of the hoisting subsystem, if it is assumed that no offset load condition exists, i.e., a₁=a₂, and further, when the anticlockwise rotation angle of the hoisting container is 0, the tension of the two steel wire ropes is consistent; and therefore, formula (30) may be simplified as(M₃₁{umlaut over (x)}_c+M₃₃{umlaut over (θ)})+(C₃₁{dot over (x)}_c+C₃₃{dot over (θ)})+(K₃₁x_c+K₃₃θ)=F₃₁  (31), wherein

in the formula, M_ij, K_ij and F_ij are respectively elements of the mass matrix, the damping matrix, the stiffness matrix and the non-potential force, i=1,2,3, and j=1,2,3.

Pose leveling of the hoisting container is regulated by two hydraulic executors, so that u₁=u=−u₂, an inclination angle θ of the hoisting container is a controlled variable, and formula (31) may be further simplified as:A{umlaut over (θ)}+B{dot over (θ)}+Cθ=Qii+Wii+Ru+F₀  (32), wherein

in the formula,

$\{\begin{array}{c}A=M_{33}\\ B=C_{33}\\ C=K_{33}\\ Q=\frac{1}{6}\rho l_{h1}{a}_1\left(1+\sin \left({\phi }_1\right)\right)+\frac{1}{6}\rho l_{h2}{a}_2\left(1+\sin \left({\phi }_2\right)\right)\\ W=\left(-\frac{1}{6}\rho {\stackrel{.}{l}}_{h1}+c_{h1}\right)a_1\left(1+\sin \left({\phi }_1\right)\right)+\left(-\frac{1}{6}\rho {\stackrel{.}{l}}_{h2}+c_{h2}\right)a_1\left(1+\sin \left({\phi }_2\right)\right)\\ R=k_{h1}{a}_1\left(1+\sin \left({\phi }_1\right)\right)+k_{h2}{a}_2\left(1+\sin \left({\phi }_2\right)\right)\\ F_0=\frac{1}{6}\rho l_{h1}{a}_1{\ddot{I}}_{\mathrm{rt}}-\frac{1}{6}\rho l_{h2}{a}_2{\ddot{I}}_{r2}+\left(-\frac{1}{6}\rho {\stackrel{.}{l}}_{h1}+c_{h1}\right)a_1{\stackrel{.}{l}}_{r1}-\\ \left(-\frac{1}{6}\rho {\stackrel{.}{l}}_{h2}+c_{h2}\right)a_2{\stackrel{.}{l}}_{r2}+k_{h1}{a}_1{l}_{\mathrm{rt}}-k_{h2}{a}_2{l}_{r2}-M_{31}{\ddot{x}}_c-\\ C_{31}{\stackrel{.}{x}}_c-K_{31}{x}_c+\frac{1}{2}\rho {\mathrm{gl}}_{h1}{a}_1-\frac{1}{2}\rho {\mathrm{gl}}_{h2}{a}_2\end{array}.$

k_h1 and k_h2 are much greater than c_h1 and c_h2, so that formula (32) may be further simplified as:A{umlaut over (θ)}+B{dot over (θ)}+Cθ=Ru+F₀  (33).

For the hoisting subsystem, a state variable is selected to be x₁=[x₁,x₂]^T=[θ,{dot over (θ)}]^T so that a dynamic model of the hoisting subsystem may be converted into a state space form:

$\begin{array}{cc}\{\begin{array}{c}{\stackrel{.}{x}}_1=x_2\\ {\stackrel{.}{x}}_2=-h_1{x}_2-h_2{x}_1+h_3{x}_3+f\end{array},\mathrm{and}& \left(34\right)\end{array}$

y₁=x₁, wherein

in the formulas, h₁=B/A, h₂=C/A, h₃=R/A, and f=F₀/A.

A building assumption of the above model is that: for the hoisting subsystem, both θ and {dot over (θ)} are bounded.

Further, the mathematical model of the electrohydraulic servo subsystem in step 2 is as follows.

The electrohydraulic servo subsystem includes a proportional servo valve in a floating hoisting sheave system and a double-outlet-rod hydraulic cylinder. It is assumed that for the electrohydraulic servo subsystem, a displacement reference signal x_p, a speed {dot over (x)}_p, an acceleration {umlaut over (x)}_p and a jerk of the hydraulic cylinder are all bounded.

A flow rate continuity equation of the double-outlet-rod hydraulic cylinder is as follows:

$\begin{array}{cc}{A}_p{\stackrel{.}{x}}_p+C_{\mathrm{tl}}{P}_L+\frac{V_t}{4{\beta }_e}{\stackrel{.}{P}}_L=Q_L,& \left(34\right)\end{array}$ wherein

in the formula, A_p is an effective acting area of a hydraulic cylinder piston, C_tl is a total leakage coefficient of the hydraulic cylinder, x_p is displacement of a hydraulic cylinder piston rod, V_t is a total volume of an oil inlet cavity and an oil return cavity of the hydraulic cylinder, β_e is an effective volume elasticity modulus of oil liquid in the hydraulic cylinder, P_L=p₁−p₂, and is load pressure drop of the hydraulic cylinder, p₁ is pressure flowing into the hydraulic cylinder, p₂ is pressure flowing out of the hydraulic cylinder, Q_L=Q₁−Q₂, and is a load flow rate, Q₁ is a flow rate flowing into the hydraulic cylinder, and Q₂ is a flow rate flowing out of the hydraulic cylinder.

According to the Newton's second law, a load force balance equation of an electrohydraulic servo system is as follows:−m{umlaut over (x)}_p−B_p{dot over (x)}_p+A_pP_L=F_L  (35),

wherein F_L is a force acting on the floating hoisting sheaves by a double-rod hydraulic cylinder, m is a total mass of the floating hoisting sheaves, and B_p is a viscous damping coefficient of the hydraulic cylinder.

For the electrohydraulic servo subsystem, a state variable is selected to be x₂=[x₃,x₄,x₅]^T=[x_p,{dot over (x)}_p,P_hL]_T, x₂=[x₃,x₄,x₅]^T=[x_p,{dot over (x)}_p,P_hL]^T so that a kinetic model of the electrohydraulic servo subsystem may be converted into a state space form:

$\begin{array}{cc}\{\begin{array}{c}{\stackrel{.}{x}}_3=x_4\\ {\stackrel{.}{x}}_4=a_1{x}_5-a_2{x}_4-a_3{F}_g\\ {\stackrel{.}{x}}_5=-a_4{x}_4-a_5{x}_5+a_6{Q}_L\end{array},& \left(36\right)\end{array}$

y₂=x₃, wherein

in the formulas, a₁=A_p/m, a₂=B_p/m, a₃=1/m, a₄=4β_eA_p/V_t, a₅=4β_eC_tl/V_t, and a₆=4β_e/V_t, so that control input u in formula (33) may be obtained.

Further, a concrete design of outputting the flatness characteristics of the nonlinear system in step 3 is as follows.

The following nonlinear system is considered:{dot over (x)}=f(x,u)  (37), wherein

in the formula, x is the system state variable, and u is the system control input with the same dimension as system output y.

If the following system output y existsy=P(x,{dot over (u)},ü, . . . u^(p))  (38),

the system state variable x and the system control input u may be expressed as equation forms of the system output and finite differential thereof:x=P(y,{dot over (y)},ÿ, . . . ,y^(q))  (39), andu=Q(y,{dot over (y)},ÿ, . . . ,y^(q+1))  (40).

Formula (37) is called as flatness. The output of this system is flatness output.

Further, a concrete design of the post leveling flatness controller of the double-rope winding type ultra-deep vertical shaft hoisting subsystem in step 4 is as follows.

According to a design method of the flatness controller, in the hoisting subsystem (34), the system output is y₁=x₁, and the system control input is u_h=x₃.

For the hoisting subsystem, a flatness equation from y₁, {dot over (y)}₁ and ÿ₁ to the system state variable x₁ and the system control input u_h is as follows:

$\begin{array}{cc}\left[\begin{array}{c}{x}_1\\ x_2\\ u_h\end{array}\right]=\left[\begin{array}{c}{y}_1\\ {\dot{y}}_1\\ \left(h_1{\dot{y}}_1+h_2{y}_1-f+{\ddot{y}}_1\right)/h_3\end{array}\right].& \left(41\right)\end{array}$

An expected state variable of the hoisting subsystem is defined according to x_1d=[x_1d,x_2d]^T=[y_1d,{dot over (y)}_1d]^T in the formula, y_1d represents the system expected output, i.e., a reference signal, and a dynamical equation of a system expected state variable x_1d is as follows:

$\begin{array}{cc}\left[\begin{array}{c}{x}_1\\ x_2\\ u_h\end{array}\right]=\left[\begin{array}{c}{y}_1\\ {\stackrel{.}{y}}_1\\ \left(h_1{\stackrel{.}{y}}_1+h_2{y}_1-f+{\ddot{y}}_1\right)h_3\end{array}\right].& \left(41\right).\end{array}$

System open-loop input u_hd is as follows:u_hd=(h₁{dot over (y)}_1d+h₂y_1d−f+ÿ_1d)/h₃  (42).

The system state tracking error is defined as z₁=[z₁,x₂]^T=[x_1d−x₁,x_2d−x₂]^T, and a dynamical equation of the system tracking error is as follows:

$\begin{array}{cc}\left[\begin{array}{c}{\stackrel{.}{z}}_1\\ {\stackrel{.}{z}}_2\end{array}\right]=\left[\begin{array}{c}{z}_2\\ -h_1{z}_2-h_2{z}_1-h_3\left(u_{\mathrm{hd}}-u_h\right)\end{array}\right].& \left(43\right).\end{array}$

If u_hd=u_h, we may acquire

$\begin{array}{cc}\left[\begin{array}{c}{\stackrel{.}{z}}_1\\ {\stackrel{.}{z}}_2\end{array}\right]=\left[\begin{array}{c}{z}_2\\ -h_1{z}_2-h_2{z}_1\end{array}\right].& \left(44\right).\end{array}$

By writing the formula as a matrix form, it is:ż₁=A_hz₁  (45), wherein

in the formula,

$A_h=\left[\begin{array}{cc}0& 1\\ -h_2& -h_1\end{array}\right].$

A_h is a Hurwitz matrix, and an error z₁ exponentially approaches to 0. An approaching speed may not be only in accordance with the open-loop control input, so that control input with state feedback is defined as

$\begin{array}{cc}{u}_h=u_{\mathrm{hd}}+\frac{1}{h_3}{K}_1{z}_1,& \left(46\right)\end{array}$

in the formula, K₁[k₁,k₂], so that a system tracking error dynamical equation with the state feedback is as follows:ż₁=A_hkz₁  (47), wherein

in the formula,

$A_{\mathrm{hk}}=\left[\begin{array}{cc}0& 1\\ -{\theta }_2-k_1& -{\theta }_1-k_2\end{array}\right].$

By properly selecting a system control gain matrix K₁, a matrix A_hk is enabled to be the Hurwitz matrix. At the moment, the system tracking error z₁ may exponentially approach to 0.

A hoisting subsystem control rule may be summarized as follows:

$\begin{array}{cc}\{\begin{array}{c}{x}_{1d}=y_{1d}\\ x_{2d}={\stackrel{.}{y}}_{1d}\\ u_{\mathrm{hd}}=\left(h_1{\stackrel{.}{y}}_{1d}+h_2{y}_{1d}-f+{\stackrel{.}{x}}_{2d}\right)/h_3\\ z_1=x_{1d}-x_1\\ z_2=x_{2d}-x_2\\ u_h=u_{\mathrm{hd}}+\frac{1}{h_3}{K}_1{z}_1\end{array}.& \left(48\right)\end{array}$

Further, a design of the position closed-loop flatness controller of the electrohydraulic servo subsystem in step 5 is as follows.

According to the electrohydraulic servo subsystem (36), the system output is y₂=y₃, and the system control input is u_L=Q_L, so that the following flatness equation of the control input u_L may be obtained:

$\begin{array}{cc}\left[\begin{array}{c}{x}_3\\ x_4\\ x_5\\ x_L\end{array}\right]=\left[\begin{array}{c}{y}_2\\ {\stackrel{.}{y}}_2\\ \frac{1}{a_1}\left({\ddot{y}}_2+a_2{\stackrel{.}{y}}_2+a_3{F}_g\right)\\ \frac{1}{a_6}\left(a_4{\stackrel{.}{y}}_2+a_5{x}_5+{\stackrel{.}{x}}_5\right)\end{array}\right].& \left(49\right)\end{array}$

The system expected state variable is defined. In the formula, y_2d is the system expected output, i.e., the reference signal. That is, a dynamical of the system expected variable x_2d=[x_3d,x_4d,x_5d]^T is:

$\begin{array}{cc}\frac{d}{\mathrm{dt}}\left[\begin{array}{c}{x}_{3d}\\ x_{4d}\\ x_{5d}\end{array}\right]=\left[\begin{array}{c}{x}_{4d}\\ a_1{x}_{5d}-a_2{x}_{4d}-a_3{F}_g\\ -a_4{x}_{4d}-a_5{x}_{5d}+a_6{u}_L\end{array}\right].& \left(50\right)\end{array}$

Thus the system open-loop input u_Ld may be obtained as follows:

$\begin{array}{cc}{u}_{\mathrm{Ld}}=\frac{1}{a_6}\left(a_4{\stackrel{.}{y}}_{2d}+a_5{x}_{5d}+{\stackrel{.}{x}}_{5d}\right).& \left(51\right)\end{array}$

The system tracking error z₂=[z₃,z₄,z₅]^T=[x_3d−x₃, x_4d−x₄,x_5d−x₅]^T is defined. Therefore, a dynamical of the system tracking error is:

$\begin{array}{cc}\left[\begin{array}{c}{\stackrel{.}{z}}_3\\ {\stackrel{.}{z}}_4\\ {\stackrel{.}{z}}_5\end{array}\right]=\left[\begin{array}{c}{z}_4\\ a_1{z}_5-a_2{z}_4\\ -a_4{z}_4-a_5{z}_5+a_6\left(u_{\mathrm{Ld}}-u_L\right)\end{array}\right].& \left(52\right)\end{array}$

When u_Ld=u_L, we may acquire

$\begin{array}{cc}\left[\begin{array}{c}{\stackrel{.}{z}}_3\\ {\stackrel{.}{z}}_4\\ {\stackrel{.}{z}}_5\end{array}\right]=\left[\begin{array}{c}{z}_4\\ a_1{z}_5-a_2{z}_4\\ -a_4{z}_4-a_5{z}_5\end{array}\right].& \left(53\right)\end{array}$

By writing the formula into a matrix form, it is:ż₂=A_Lz₂  (54), wherein

in the formula,

$A_L=\left[\begin{array}{ccc}0& 1& 0\\ 0& -a_2& a_1\\ 0& -a_4& -a_5\end{array}\right].$

Further, the control input with the state feedback is defined as

$\begin{array}{cc}{u}_L=u_{\mathrm{Ld}}+\frac{1}{a_6}{K}_2{z}_2,& \left(55\right)\end{array}$

in the formula, K₂[k₃,k₄,k₅]^T. A tracking error dynamical equation with the state feedback is as follows:ż₂=A_Lkz₂  (56), wherein

in the formula,

$A_{\mathrm{Lk}}=\left[\begin{array}{ccc}0& 1& 0\\ 0& -a_2& a_1\\ -k_3& -a_4-k_4& -a_5-k_5\end{array}\right].$

The proper control gain matrix K₂ is selected so that the matrix A_LK is the Hurwitz matrix, and the system tracking error z₂ exponentially approaches to 0. Therefore, the following control formula of the electrohydraulic servo subsystem is obtained:

$\begin{array}{cc}\{\begin{array}{c}{x}_{3d}=y_{2d}\\ x_{4d}={\stackrel{.}{y}}_{2d}\\ x_{5d}=\frac{1}{a_6}\left({\ddot{y}}_{2d}+a_4{\stackrel{.}{y}}_{2d}+a_5{y}_{2d}-a_3{F}_g\right)\\ u_{\mathrm{Ld}}=\frac{1}{a_6}\left(a_4{x}_{4d}+a_5{x}_{5d}+{\stackrel{.}{x}}_{5d}\right)\\ z_3=x_{3d}-x_3\\ z_4=x_{4d}-x_4\\ z_5=x_{5d}-x_5\\ u_L=u_{\mathrm{Ld}}+\frac{1}{a_6}{K}_2{z}_2\end{array}.& \left(57\right)\end{array}$

Compared with an existing popular design method of the backstepping controller, the present invention has the advantages that the derivation process of the system state variables is omitted, so that the design process of the controller is greatly simplified; the response time of the controller may be shortened, and the hoisting container may fast reach a leveling state; in an application process of the system, sensor measurement noise and system non-modeling characteristics may be amplified through state variable derivation, so that the tracking errors may be reduced through the design of the flatness controller; the control process is more precise; and good control performance is ensured.

BRIEF DESCRIPTION OF THE DRAWINGS

FIG. 1 is a schematic structural diagram of a hoisting system of the present invention.

FIG. 2 is a kinetic model diagram of a double-outlet-rod hydraulic cylinder.

FIG. 3 is a structural block diagram of a control system of the present invention.

FIG. 4 is a comparison diagram of angle tracking signals of a hoisting container of a flatness controller in a concrete embodiment of the present invention.

FIG. 5 is a partial enlarged diagram of the angle tracking signals of the hoisting container of the flatness controller in the concrete embodiment of the present invention.

FIG. 6 is a comparison diagram of tracking signals of a hydraulic cylinder 1 of the flatness controller in the concrete embodiment of the present invention.

FIG. 7 is a tracking error diagram of the hydraulic cylinder 1 of the flatness controller in the concrete embodiment of the present invention.

FIG. 8 is a comparison diagram of tracking signals of a hydraulic cylinder 2 of the flatness controller in the concrete embodiment of the present invention.

FIG. 9 is a tracking error diagram of the hydraulic cylinder 2 of the flatness controller in the concrete embodiment of the present invention.

FIG. 10 is a comparison diagram of angle tracking signals of a hoisting container of a backstepping controller in the concrete embodiment of the present invention.

FIG. 11 is a partial enlarged diagram of the angle tracking signals of the hoisting container of the backstepping controller in the concrete embodiment.

FIG. 12 is a comparison diagram of tracking signals of a hydraulic cylinder 1 of the backstepping controller in the concrete embodiment.

FIG. 13 is a tracking error diagram of the hydraulic cylinder 1 of a backstepping controller in the concrete embodiment.

FIG. 14 is a comparison diagram of tracking signals of a hydraulic cylinder 2 of the backstepping controller in the concrete embodiment.

FIG. 15 is a tracking error diagram of the hydraulic cylinder 2 of the backstepping controller in the concrete embodiment.

DETAILED DESCRIPTION OF THE INVENTION

The present invention will be described in detail with reference to the accompanying drawings and a concrete embodiment.

As shown in FIG. 1 and FIG. 2, for an oil source pressure P_s of a hydraulic system, P_s=15*10⁶ Pa. For an effective acting area A_p of a double-outlet-rod hydraulic cylinder 4, A_p=1.88*10⁻³ m². For a load mass m of the hydraulic system, m=200 kg. For a viscous damping coefficient B_p of the hydraulic system, B_p=25000 N(m/s). For a total volume V_t of an oil inlet cavity and an oil return cavity of the hydraulic cylinder, V_t=0.96*10⁻³ m³. For a total leakage coefficient C_t1 of the hydraulic system, C_t1=9.2*10⁻¹³ m³/(s/Pa). For a volume elasticity modulus β_e of hydraulic oil, β_e=6.9*10⁸ Pa. For vertical distances b₁ and b₂ from upper and lower surfaces of a hoisting container 6 to a gravity center of the hoisting container, b₁=b₂=0.0625 m. For horizontal distances a₁ and a₂ from connecting points of two vertical section steel wire ropes 5 on the hoisting container 6 to the gravity center of the hoisting container, a₁=a₂=0.1575 m. For initial lengths l_h20 and l_h20 of the vertical section steel wire ropes 5, l_h20=l_h20=6 m. For a rotational inertia I_c of the hoisting container 6, I_c=3.307 kg·m⁻². For a unit length mass ρ of the steel wire rope, ρ=0.417 kg/m. For inclination angles a₁ and a₂ of left and right string ropes 2, a₁=a₂=64.5°. For radii r₁ and r₂ of two floating hoisting sheaves 3, r₁=r₂=0.2 m. For masses m₁ and m₂ of the two floating hoisting sheaves 3, m₁=m₂=10 kg. For a mass m_c of the hoisting container 6, m_c=120 kg. For transverse equivalent damping coefficients c_s1, c_s2, c_s3 and c_s4 of four pairs of spring-damping models, c_s1=c_s2=c_s3=c_s4=10 N/(m/s). For transverse equivalent stiffness k_s1, k_s2, k_s3 and k_s4 of the four pairs of spring-damping models, k_s1=k_s2=k_s3=k_s4=1000 Pa.

For control parameters of a flatness controller, K₁=[k₁,k₂]=[20,10], and K₂=[k₃,k₄,k₅]=[3*10¹⁴,2*10¹²,2].

For control parameters of a backstepping controller, k₁=20, k₂=20, k₃=300, k₄=280, and k₅=260.

An initial angle of the hoisting container is set to be 5°.

As shown in FIG. 3, the steps of leveling the hoisting container of the flatness controller are as follows:

1) A state space form of a kinetic model of a hoisting subsystem is:

$\begin{array}{cc}\{\begin{array}{c}{\stackrel{.}{x}}_1=x_2\\ {\stackrel{.}{x}}_2=-h_1{x}_2-h_2{x}_1+h_3{x}_3+f\end{array},& \left(34\right)\end{array}$

y₁=x₁, wherein

in the formula, h₁=B/A, h₂=C/A, h₃=R/A, and f=F₀/A.

2) A state space form of a kinetic model of an electrohydraulic servo subsystem is:

$\begin{array}{cc}\{\begin{array}{c}{\stackrel{.}{x}}_3=x_4\\ {\stackrel{.}{x}}_4=a_1{x}_5-a_2{x}_4-a_3{F}_g\\ {\stackrel{.}{x}}_5=-a_4{x}_4-a_5{x}_5+a_6{Q}_L\end{array},& \left(36\right)\end{array}$

y₂=x₃, wherein

in the formula, a₁=A_p/m, a₂=B_p/m, a₃=1/m, a₄=4β_eA_p/V_t, a₅=4β_eC_tl/V_t and a₆=4β_e/V_t.

3) A system state variable x and a system control input u may be expressed as the following equation form of the system flatness characteristic output and a finite differential thereof:x=P(y,{dot over (y)},ÿ, . . . y^(q))  (39), andu=Q(y,{dot over (y)},ÿ, . . . ,y^(q))  (40).

4) A concrete design of a pose leveling flatness controller of a double-rope winding type ultra-deep vertical shaft hoisting subsystem is as follows:

$\begin{array}{cc}\{\begin{array}{c}{x}_{1d}=y_{1d}\\ x_{2d}={\stackrel{.}{y}}_{1d}\\ u_{\mathrm{hd}}=\left(h_1{\stackrel{.}{y}}_{1d}+h_2{y}_{1d}-f+{\stackrel{.}{x}}_{2d}\right)/h_3\\ z_1=x_{1d}-x_1\\ z_2=x_{2d}-x_2\\ u_h=u_{\mathrm{hd}}+\frac{1}{h_3}{K}_1{z}_1\end{array}.& \left(47\right)\end{array}$

5) A design of a position closed-loop flatness controller of the electrohydraulic servo subsystem is as follows:

$\begin{array}{cc}\{\begin{array}{c}{x}_{3d}=y_{2d}\\ x_{4d}={\stackrel{.}{y}}_{2d}\\ x_{5d}=\frac{1}{a_6}\left({\ddot{y}}_{2d}+a_4{\stackrel{.}{y}}_{2d}+a_5{y}_{2d}-a_3{F}_g\right)\\ u_{\mathrm{Ld}}=\frac{1}{a_6}\left(a_4{x}_{4d}+a_5{x}_{5d}+{\stackrel{.}{x}}_{5d}\right)\\ z_3=x_{3d}-x_3\\ z_4=x_{4d}-x_4\\ z_5=x_{5d}-x_5\\ u_L=u_{\mathrm{Ld}}+\frac{1}{a_6}{K}_2{z}_2\end{array}.& \left(57\right)\end{array}$

According to parameter input of the concrete embodiment, the obtained leveling performance of the hoisting container of the flatness controller is shown in FIG. 4 to FIG. 9.

A pose leveling control design of the hoisting container of the backstepping controller is as follows:

$\begin{array}{cc}\{\begin{array}{c}{z}_1=x_{1d}-x_{1r}\\ z_2=x_{2d}-{\alpha }_1\\ {\alpha }_1=k_1{z}_1+{\stackrel{.}{x}}_{1r}\\ u_h=\frac{1}{h_3}\left(h_1{x}_2+h_2{x}_1-f+{\stackrel{.}{\alpha }}_1-k_2{z}_2+z_1\right)\end{array}.& \left(48\right)\end{array}$

A position closed-loop control process of the electrohydraulic servo subsystem of the backstepping controller is as follows:

$\begin{array}{cc}\{\begin{array}{c}{z}_3=x_{3d}-x_3\\ z_4={\alpha }_3-x_4\\ z_5={\alpha }_4-x_5\\ {\alpha }_3=-k_3{z}_3+{\stackrel{.}{x}}_{3d}\\ {\alpha }_4=\frac{1}{a_1}\left(z_3+a_2{x}_2-\frac{F_g}{a_3}+{\stackrel{.}{\alpha }}_3+k_4{z}_4\right)\\ u_L=\frac{1}{a_6}\left(k_5{z}_5+{\stackrel{.}{\alpha }}_4+a_4{x}_2+a_5{x}_3+a_1{z}_4\right)\end{array}.& \left(58\right)\end{array}$

According to parameter input in the concrete embodiment, leveling performance of the hoisting container of the backstepping controller is shown in FIG. 10 to FIG. 15.

From the angle tracking performance of the hoisting containers of the two controllers, the hoisting containers may both reach a leveling state in a certain time, but the flatness controller enables the hoisting container to reach the leveling state in 70 ms, and the backstepping controller enables the hoisting container to reach a stable state in 450 ms. From the position tracking performance of two hydraulic cylinders, the tracking error of the backstepping controller is greater than that of the flatness controller. Based on the above, the control performance of the flatness controller is superior to that of the backstepping controller.

Claims

1. A hoisting container pose control method of a double-rope winding type ultra-deep vertical shaft hoisting system, comprising: step 1, building a mathematical model of a double-rope winding type ultra-deep vertical shaft hoisting subsystem;step 2, building a position closed-loop mathematical model of an electrohydraulic servo subsystem;step 3, outputting flatness characteristics of a nonlinear system;step 4, designing a flatness controller of the double-rope winding type ultra-deep vertical shaft hoisting subsystem based on the mathematical model;step 5, designing a position closed-loop flatness controller of the electrohydraulic servo subsystem based on the position closed-loop mathematical model; andstep 6, controlling a hoisting container based on the flatness controller, the position closed-loop flatness controller, and the flatness characteristics of the nonlinear system,wherein the mathematical model of the double-rope winding type ultra-deep vertical shaft hoisting subsystem in step 1 is as follows: M{umlaut over (q)}+C{dot over (q)}+Kq=F  (1-1), whereinin the formula, {umlaut over (q)},{dot over (q)} and q are respectively a generalized acceleration, speed and displacement, q=[xc,yc,θ], xc and yc are respectively a vertical displacement and a horizontal displacement of a gravity center of the hoisting container, θ is an anticlockwise rotation angle of the hoisting container, and M, C, K and F are respectively a mass matrix, a damping matrix, a stiffness matrix and a non-potential force of the hoisting subsystem wherein

2. The hoisting container pose control method of the double-rope winding type ultra-deep vertical shaft hoisting system according to claim 1, wherein in the modeling process of the hoisting subsystem, if it is assumed that no offset load condition exists, i.e., a1=a2, and when the anticlockwise rotation angle of the hoisting container is 0, the tension of two steel wire ropes is consistent; and therefore, the mathematical model of the double-rope winding type ultra-deep vertical shaft hoisting subsystem is simplified as: (M31{umlaut over (x)}c+M33{umlaut over (θ)})+(C31{dot over (x)}c+C33{dot over (θ)})+(K31xc+K33θ)=F31  (3-1), whereinin the formula, Mij, Cij, Kij and Fij are respectively elements of the mass matrix, the damping matrix, the stiffness matrix and the non-potential force, i=1,2,3, and j=1,2,3, xc is the vertical displacement of the gravity center of the hoisting container.

3. The hoisting container pose control method of the double-rope winding type ultra-deep vertical shaft hoisting system according to claim 2, wherein a pose leveling of the hoisting container is regulated by two hydraulic executors, so that u1=u=−u2, an inclination angle θ of the hoisting container is a controlled variable, and the mathematical model of the double-rope winding type ultra-deep vertical shaft hoisting subsystem is further simplified as: A{umlaut over (θ)}+B{dot over (θ)}+Cθ=Qii+Wii+Ru+F0  (4-1), whereinin the formula (4-1),

4. The hoisting container pose control method of the double-rope winding type ultra-deep vertical shaft hoisting system according to claim 3, wherein a state variable is selected to be x1=[x1,x2]T=[θ, {dot over (θ)}]T, so that a dynamic model of the hoisting subsystem may be converted into a state space form:

5. The hoisting container pose control method of the double-rope winding type ultra-deep vertical shaft hoisting system according to claim 1, wherein the mathematical model of the electrohydraulic servo subsystem in step 2 is as follows:

6. The hoisting container pose control method of the double-rope winding type ultra-deep vertical shaft hoisting system according to claim 4, wherein a state variable is selected to be x2=[x3,x4,x5]T[xp,{dot over (x)}p,PL]T, so that a kinetic model of the electrohydraulic servo subsystem may be converted into a state space form:

7. The hoisting container pose control method of the double-rope winding type ultra-deep vertical shaft hoisting system according to claim 1, wherein a concrete design of outputting the flatness characteristics of the nonlinear system in step 3 is as follows: {dot over (x)}=f(x,u)  (7-2), whereinin the formula (7-2), x is a system state variable, and u is a system control input with a same dimension as system output y;if the following system output y exists: y=P(x,{dot over (u)},ü, . . . ,u(p))  (7-3),the system state variable x and the system control input u may be expressed as equation forms of the system output and finite differential thereof: x=P(y,{dot over (y)},ÿ, . . . ,y(q))  (7-4), andU=Q(y,{dot over (y)},ÿ, . . . ,y(q+1))  (7-5)wherein P is a control variable matrix Q is a control output matrix.

8. The hoisting container pose control method of the double-rope winding type ultra-deep vertical shaft hoisting system according to claim 1, wherein a concrete design of the post leveling flatness controller of the double-rope winding type ultra deep vertical shaft hoisting subsystem in step 4 is as follows:

9. The hoisting container pose control method of the double-rope winding type ultra-deep vertical shaft hoisting system according to claim 1, wherein a design of the position closed-loop flatness controller of the electrohydraulic servo subsystem in step 5 is as follows: