Method of emulsion concentration optimization for cold continuous rolling mill set

Abstract

Disclosed is a method of emulsion concentration optimization for a cold continuous rolling mill set for achieving vibration suppression, the method comprising: defining the process parameters involved in the process of emulsion concentration optimization; setting an initial set value of an emulsion concentration comprehensive optimization target function for a cold continuous rolling mill set for achieving vibration suppression; calculating a bite angle of each stand; calculating a vibration determination index reference value of each stand; setting the emulsion concentration of each stand; calculating the outlet temperature of a strip steel of each stand; calculating the dynamic viscosity of an emulsion in a roll gap of each stand; calculating the oil film thickness in the roll gap of each stand; calculating the emulsion concentration comprehensive optimization target function; determining whether the inequation F(X)<F.sub.0 is established; determining whether the concentration of the emulsion exceeds a feasible region range, and outputting the optimal emulsion concentration set value.

Claims

1. A method of emulsion concentration optimization for a cold continuous rolling mill set, comprising the following steps: (a) acquiring apparatus characteristic parameters of a cold continuous rolling mill set; (b) acquiring critical rolling process parameters of a strip material; (c) acquiring process parameters involved in the process of emulsion concentration optimization; (d) setting an initial set value of an emulsion concentration comprehensive optimization target function for a cold continuous rolling mill set for achieving vibration suppression: F.sub.0=1.0×10.sup.10; the executing order of steps (a) to (d) is not limited; (e) calculating a bite angle α, of each stand; (f) calculating a vibration determination index reference value ξ.sub.0i of each stand; (g) setting an emulsion concentration C.sub.i of each stand; (h) calculating the outlet temperature T.sub.i of a strip steel of each stand; (i) calculating the dynamic viscosity η.sub.0i of an emulsion in a roll gap of each stand; (j) calculating an oil film thickness ξ.sub.i in the roll gap of each stand; (k) calculating the emulsion concentration comprehensive optimization target function F(X); (l) determining whether the inequation F(X)<F.sub.0 is established, if yes, then setting C.sub.i.sup.y=C.sub.i, F.sub.0=F(X) and turning to step (m); if no, directly turning to step (m); (m) determining whether the emulsion concentration C.sub.i exceeds the range of a feasible region, if yes, turning to step (n); if no, turning to step (g), wherein the feasible region refers to a region from 0 to the maximum emulsion concentration allowed by the cold continuous rolling mill set; (n) outputting the optimal emulsion concentration set value C.sub.i.sup.y, wherein C.sub.i.sup.y is the value of C.sub.i when the calculated value of F(X) is minimum in the feasible region; and (o) adjusting and controlling the emulsion concentration of each stand according to the optimal emulsion concentration set value C.sub.i.sup.y in the step (n) by a control system of the cold continuous rolling mill set; and in each formula, i represents the stand ordinal number of the cold continuous rolling mill set.

2. The method of claim 1, wherein calculating the vibration determination index reference value ξ.sub.0i of each stand in the step (f) comprising the following steps: (f1) calculating an over-lubricated oil film thickness critical value ξ.sub.i.sup.+ of each stand as follows: it is assumed that when $\frac{{\gamma }_i}{{\alpha }_i}=A^{+},$ the roll gap is just in an over-lubricated status, wherein γ.sub.i is a neutral angle of each stand, and A.sup.+ is an over-lubricated determining coefficient; calculating to obtain $u_i^{+}=\frac{1}{2\left(2A^{+}-1\right)}\left(\sqrt{\frac{\Delta h_i}{R_i^{\prime }}}+\frac{T_{i0}-T_{i1}}{P_i}\right)$ according to ${\alpha }_i=\sqrt{\frac{{\Delta h}_i}{R_i^{\prime }}},$ wherein Δh.sub.i is the rolling reduction, Δh.sub.i=h.sub.0i−h.sub.1i, h.sub.0i is the inlet thickness of each stand, h.sub.1i is the outlet thickness of each stand, and R.sub.i′ is the flattening radius of a work roll of the i.sup.th stand, and ${\gamma }_i=\frac{1}{2}\sqrt{\frac{\Delta h_i}{R_i^{\prime }}}\left[1+\frac{1}{2u_i}\left(\sqrt{\frac{\Delta h_i}{R_i^{\prime }}}+\frac{T_{i0}-T_{i1}}{P_i}\right)\right],$ wherein T.sub.0i is the back tension of each stand, T.sub.1i is the front tension of each stand, and P.sub.i is the rolling pressure of each stand; then calculating to obtain the over-lubricated oil film thickness critical value of each stand ξ.sub.i.sup.+ by ${\xi }_1^{+}=\frac{1}{B_i}\ln \frac{u_i^{+}-a_i}{b_i}$ according to the relationship formula between the friction coefficient and the oil film thickness: u.sub.i=a.sub.i+b.sub.i.Math.e.sup.B.sup.i.sup..Math.ξ.sup.i, wherein a.sub.i is the liquid friction influence coefficient, b.sub.i is the dry friction influence coefficient, and B.sub.i is the friction coefficient attenuation index; (f2) calculating an under-lubricated oil film thickness critical value ξ.sub.i.sup.− of each stand as follows: calculating to obtain $u_i^{-}=\frac{1}{2\left(2A^{-}-1\right)}\left(\sqrt{\frac{\Delta h_i}{R_i^{\prime }}}+\frac{T_{i0}-T_{i1}}{P_i}\right)$ assuming that when $\frac{{\gamma }_i}{{\alpha }_i}=A^{-},$ the roll gap is just in an under-lubricated status, wherein A.sup.− is the under-lubricated determining coefficient; then calculating to obtain the under-lubricated oil film thickness critical value ξ.sub.i.sup.− of each stand by ${\xi }_i^{-}=\frac{1}{B_i}\ln \frac{u_i^{-}-a_i}{b_i};$ and (f3) calculating the vibration determination index reference value ξ.sub.0i by ${\xi }_{0i}=\frac{{\xi }_i^{+}+{\xi }_i^{-}}{2}.$

3. The method of claim 1, wherein calculating the outlet temperature T.sub.i of the strip steel of each stand in the step (h) comprising the following steps: (h1) calculating the outlet temperature T.sub.i of the first stand: $T_1=T_1^{\mathrm{Inlct}}+\frac{1-\left({\epsilon }_1/4\right)}{1-\left({\epsilon }_1/2\right)}.Math.\frac{K_1\ln \left(\frac{1}{1-{\epsilon }_1}\right)}{\rho SJ},$ wherein T.sub.1.sup.Inlet is the inlet temperature of each stand, ${\epsilon }_i=\frac{\Delta h_i}{h_{0i}},$ Δh.sub.i=h.sub.0i−h.sub.1ih.sub.0i is the inlet thickness of each stand, h.sub.1i is the outlet thickness of each stand, ρ is the density of strip steel, S is the specific heat capacity of strip steel, J is the mechanical equivalent of heat, and K.sub.i is the resistance to deformation of the strip steel of each stand; (h2) setting i to 1; (h3) setting T.sub.i, 1 the temperature of the first section of strip steel behind the outlet of the i.sup.th stand, i.e., T.sub.i, 1=T.sub.i; (h4) setting j to 2; (h5) calculating the temperature T.sub.i,j of the j.sup.th section of strip steel by the relationship between the temperature of the j.sup.th section and the temperature of the j−1.sup.th section shown by the following equation: $T_{i,j}=-\frac{2k_0{w}^{0.264}\exp \left(9.45-0.1918C_i\right)\times 1.163l}{v_{1i}{h}_{1i}\rho \mathrm{Sm}}{T}_{i,j-1}^{-0.213}\left(T_{i,j-1}-T_c\right)+T_{i,j-1},$ wherein k.sub.0 is the influence coefficient of nozzle shape and spraying angle, w is the flow rate of the emulsion, l is a distance between stands, and the distance l between stands is equally divided into m section, the temperature in the section is represented by T.sub.i, j, v.sub.1i is the outlet speed of each stand, h.sub.1i is the outlet thickness of each stand, ρ is the density of the strip steel, S is the specific heat capacity of the strip steel, T.sub.i is the outlet temperature of each stand, and T.sub.c is the temperature of the emulsion; (h6) determining whether the inequation j<m is established, if yes, then setting j=j+1 and turning to the step (h5); if no, turning to step (h7); (h7) obtaining the temperature T.sub.i,m of the m.sup.th section via iterative calculation; (h8) calculating the inlet temperature T.sub.i+1.sup.Inlet of the i+1.sup.th stand:
T.sub.i+1.sup.Inlet=T.sub.i,m; (h9) calculating the outlet temperature T.sub.i+1.sup.Inlet of the i+1.sup.th stand: $T_{i+1}=T_{i+1}^{\mathrm{Inlet}}+\frac{1-\left({\epsilon }_{i+1}/4\right)}{1-\left({\epsilon }_{i+1}/2\right)}.Math.\frac{K_{i+1}\ln \left(\frac{1}{1-{\epsilon }_{i+1}}\right)}{\rho \mathrm{SJ}};$ (h10) determining whether the inequation i<n is established, if yes, setting i=i+1 and turning to the step (h3); if no, turning to step (h11); and (h11) obtaining the outlet temperature T.sub.i of each stand.

4. The method of claim 1, wherein the apparatus characteristic parameters of the cold continuous rolling mill set at least comprise: the radius R.sub.i of a work roll of each stand; the surface linear speed v.sub.ri of a roll of each stand; the original roughness Ra.sub.ir0 of a work roll of each stand; the roughness attenuation coefficient B.sub.L of a work roll; the distance l between stands; and rolling kilometers L.sub.i of a work roll of each stand after roll change; wherein i=1, 2, . . . , n; i represents the ordinal number of the stand of the cold continuous rolling mill set, and n is the total number of the stands.

5. The method of emulsion concentration optimization for the cold continuous rolling mill set as claimed in claim 1, wherein the critical rolling process parameters of the strip material at least comprise: the inlet thickness h.sub.0i of each stand; the outlet thickness h.sub.1i of each stand; the width B of the strip steel; the inlet speed v.sub.0i of each stand; the outlet speed v.sub.1i of each stand; the inlet temperature T.sub.1.sup.Inlet; the resistance to deformation K.sub.i of the strip steel of each stand; the rolling pressure P.sub.i of each stand; the back tension T.sub.0i of each stand; the front tension T.sub.1i of each stand; the concentration influence coefficient k.sub.c of the emulsion; the viscosity compression coefficient θ of a lubricant; the density ρ of the strip steel; the specific heat capacity S of the strip steel; the flow rate w of the emulsion; the temperature T.sub.c of the emulsion; and the mechanical equivalent of heat J.

6. The method of claim 1, wherein the process parameters involved in the process of emulsion concentration optimization at least comprise: the over-lubricated oil film thickness critical value ξ.sub.i.sup.+ and the corresponding friction coefficient u.sub.i.sup.+ of each stand; the under-lubricated oil film thickness critical value ξ.sub.i.sup.− and the corresponding friction coefficient u.sub.i.sup.− of each stand; and the vibration determination index reference value ξ.sub.0i; the rolling reduction Δh.sub.i=h.sub.0i−h.sub.1i; the rolling reduction ratio ${\epsilon }_i=\frac{\Delta h_i}{h_{0i}};$ the inlet temperature T.sub.i.sup.Inlet and the outlet temperature T.sub.i of each stand; the distance l between stands, which is equally divided into m section, the temperature in the section represented by T.sub.i, j, wherein 1≤j≤m and T.sub.i.sup.Inlet=T.sub.i−1,m; the over-lubricated determining coefficient A.sup.+; and the under-lubricated determining coefficient A.sup.−.

7. The method of claim 1, wherein the calculation formula for calculating the bite angle α.sub.i of each stand is as follows: ${\alpha }_i=\sqrt{\frac{\Delta h_i}{R_i^{\prime }}}$ wherein R.sub.i′ is the flattening radius of the work roll of the i.sup.th stand, and is a process value in rolling pressure calculation.

8. The method of claim 1, wherein the calculation formula for calculating the dynamic viscosity η.sub.0i of the emulsion in the roll gap of each stand is as follows:
η.sub.0i=b.Math.exp(−a.Math.T.sub.i) wherein a and b are dynamic viscosity parameters of the lubricant under atmospheric pressure.

9. The method of claim 1, wherein the calculation formula for calculating the oil film thickness in the roll gap of each stand is as follows: ${\xi }_i=\frac{h_{0i}+h_{1i}}{2h_{0i}}.Math.k_c.Math.\frac{3\theta {\eta }_{0i}\left(v_{\mathrm{ri}}+v_{0i}\right)}{{\alpha }_i\left[1-e^{-\theta \left(K_i\frac{T_{0i}}{h_{0i}.Math.B}\right)}\right]}-k_{\mathrm{rg}}.Math.\left(1+K_{\mathrm{rs}}\right).Math.{\mathrm{Ra}}_{\mathrm{ir}0}.Math.e^{-B_{\mathrm{Li}}.Math.L_i},$ wherein h.sub.0i is the inlet thickness of each stand, h.sub.1i is the outlet thickness of each stand, k.sub.c is the emulsion concentration influence coefficient, θ is the viscosity compression coefficient of the lubricant, K.sub.i is the resistance to deformation of the strip steel of each stand, η.sub.0i is the dynamic viscosity of the emulsion in the roll gap of each stand, v.sub.0i is the inlet speed of each stand, v.sub.ri is the surface linear speed of a roll of each stand, T.sub.0i is the back tension of each stand, B is the width of the strip steel, k.sub.rg represents the coefficient of the strength of entrainment of lubricant by the longitudinal surface roughness of the work roll and the strip steel, the value of which is from 0.09 to 0.15, K.sub.rs represents the impression rate, i.e., the ratio of transmitting surface roughness of the work roll to the strip steel, Ra.sub.ir0 is the original roughness of a work roll of each stand, B.sub.L is the roughness attenuation coefficient of the work roll, and L.sub.i is the rolling kilometers of a work roll of each stand after roll change.

10. The method of in claim 1, wherein the emulsion concentration comprehensive optimization target function is calculated according to the following formula: $\{\begin{array}{c}F\left(X\right)=\frac{\lambda }{n}\underset{i=1}{\overset{n}{.Math.}}\sqrt{{\left({\xi }_i-{\xi }_{0i}\right)}^2}+\left(1-\lambda \right)\max .Math.{\xi }_i-{\zeta }_{0i}.Math.\\ {\xi }_i^{-}<{\xi }_i<{\xi }_i^{+}\end{array},$ wherein X={C.sub.i} is an optimization variable, and λ is a distribution coefficient.

Description

BRIEF DESCRIPTION OF THE DRAWINGS

(1) FIG. 1 is a schematic flow diagram of the general technical solutions according to the present invention;

(2) FIG. 2 is a schematic diagram of the calculation process of the reference value of the vibration determination index according to the present invention; and

(3) FIG. 3 is a schematic diagram of the calculation process of the strip steel outlet temperature of each stand according to the present invention.

DETAILED DESCRIPTION

(4) The invention will be further described below in conjunction with the accompany drawings and embodiments.

(5) In order to further explain the application process of the related technologies mentioned in the invention, a 1730 cold continuous rolling mill set of a cold rolling plant is taken as an example. The application process of the method of emulsion concentration optimization for a cold continuous rolling mill set for achieving vibration suppression is described in detail.

(6) At first, according to the various steps shown in FIG. 1, the relevant parameters are determined in turn. Then the parameters are substituted into corresponding formulas for calculation, and the desired optimal emulsion concentration set value C.sub.i.sup.y is determined or obtained. Finally, the emulsion concentration of each stand is controlled according to the determined optimal emulsion concentration set value, and the comprehensive optimization control is carried out to achieve suppressing the vibration of the rolling mill.

(7) Specifically, in the step (a), the acquired apparatus characteristic parameters of a cold continuous rolling mill set mainly include:

(8) the radius of a work roll of each stand: R.sub.i={210, 212, 230, 230, 228} mm;

(9) the surface linear speed of a roll of each stand: v.sub.ri={180, 320, 500, 800, 1150} m/min;

(10) the original roughness of a work roll of each stand: Ra.sub.ir0={1.0, 1.0, 0.8, 0.8, 1.0} um;

(11) the roughness attenuation coefficient of the work roll: B.sub.L=0.01;

(12) the distance between stands: l=2700 mm; and

(13) the rolling kilometers of a work roll of each stand after roll change: L.sub.i={100, 110, 230, 180, 90} km; wherein i=1, 2, . . . , n; i represents the ordinal number of the stand of the cold continuous rolling mill set; and n=5, which is the total number of the stands, the same below;

(14) subsequently, in the step (b), the acquired critical rolling process parameters of the strip material mainly include:

(15) the inlet thickness of each stand: h.sub.0i={2.0, 1.14, 0.63, 0.43, 0.28} mm;

(16) the outlet thickness of each stand: h.sub.1i={1.14, 0.63, 0.43, 0.28, 0.18} mm;

(17) the width of the strip steel: B=966 mm;

(18) the inlet speed of each stand: v.sub.0i={110, 190, 342, 552, 848} m/min;

(19) the outlet speed of each stand: v.sub.1i={190, 342, 552, 848, 1214} m/min;

(20) the inlet temperature: T.sub.1.sup.Inlet=10° C.;

(21) the resistance to deformation of the strip steel of each stand:

(22) K.sub.i={36, 40, 480, 590, 650} MPa;

(23) the rolling pressure of each stand: P.sub.i={12800, 11300, 10500, 9600, 8800} kN;

(24) the back tension of each stand: T.sub.0i={70, 145, 208, 202, 229} MPa;

(25) the front tension of each stand: T.sub.1i={145, 208, 202, 229, 56} MPa;

(26) the concentration influence coefficient of the emulsion: k.sub.c=0.9;

(27) the viscosity compression coefficient of the lubricant: θ=0.034;

(28) the density of the strip steel: ρ=7800 kg/m.sup.3;

(29) the specific heat capacity of the strip steel: S=0.47 kJ/(kg.Math.° C.);

(30) the flow rate of the emulsion: w=900 m/min;

(31) the temperature of the emulsion: T.sub.c=58° C.;

(32) the mechanical equivalent of heat: J=1; and

(33) the flattening radius of the work roll of the it stand: R.sub.i′={278.2, 279.7, 300.5, 301.6, 295.4};

(34) subsequently, in the step (c), the acquired process parameters involved in the process of emulsion concentration optimization mainly include: the over-lubricated oil film thickness critical value ξ.sub.i.sup.+ and the corresponding friction coefficient u.sub.i.sup.+ of each stand; the under-lubricated oil film thickness critical value ξ.sub.i.sup.− and the corresponding friction coefficient u.sub.i.sup.− of each stand; the vibration determination index reference value ξ.sub.0i, the rolling reduction: Δh.sub.i=h.sub.0i−h.sub.1i={0.86, 0.51, 0.2, 0.15, 0.1}; the rolling reduction ratio:

(35) ${\epsilon }_i=\frac{\Delta h_i}{h_{0i}}=\left\{0.43,0.45,0.32,0.35,0.36\right\};$
the inlet temperature T.sub.i.sup.Inlet each stand; and the outlet temperature T.sub.i of each stand; the distance l between stands is 2700 mm, which is equally divided into m=30 sections, the temperature in the section is represented by T.sub.i, j (wherein 1≤j≤m), and T.sub.i.sup.Inlet=T.sub.i−1,m; the over-lubricated determining coefficient A.sup.+; and the under-lubricated determining coefficient A.sup.−.

(36) subsequently, in the step (d), an initial set value F.sub.0=1.0×10.sup.10 of an emulsion concentration comprehensive optimization target function for a cold continuous rolling mill set for achieving vibration suppression is set;

(37) subsequently, in the step (e), the bite angle α.sub.i of each stand is calculated according to the rolling theory using the calculation formula:

(38) ${\alpha }_i=\sqrt{\frac{\Delta h_i}{R_i^{\prime }}},$
obtaining α.sub.i={0.0556, 0.0427, 0.0258, 0.0223, 0.0184};

(39) subsequently, in the step (f), the vibration determination index reference value ξ.sub.0i of each stand is calculated according to the sub-steps shown in the FIG. 2:

(40) (f1) calculating the over-lubricated oil film thickness critical value ξ.sub.i.sup.+ of each stand:

(41) it is assumed that when

(42) 0$\frac{{\gamma }_i}{{\alpha }_i}=A^{+}=1,$
the roll gap is just in an over-lubricated status; according to

(43) ${\alpha }_i=\sqrt{\frac{\Delta h_i}{R_i^{\prime }}}$
and the calculation formula of the neutral angle γ.sub.i of each stand,

(44) $u_i^{+}=\frac{1}{2\left(2A^{+}-1\right)}\left(\sqrt{\frac{\Delta h_i}{R_i^{\prime }}}+\frac{T_{i0}-T_{i1}}{P_i}\right)$
is obtained, obtaining u.sub.i.sup.+={00248, 0.0186, 0.0132, 0.0136, 0.0191};

(45) according to the relationship between the friction coefficient and the oil film thickness: u.sub.i=a.sub.i+b.sub.i.Math.e.sup.B.sup.i.sup..Math.ξ.sup.i (in the embodiment, a.sub.i=0.0126, b.sub.i=0.1416, and B.sub.i=−2.4297), the over-lubricated oil film thickness critical value ξ.sub.i.sup.+ of each stand is calculated by the calculation formula:

(46) ${\xi }_i^{+}=\frac{1}{B_i}\ln \frac{u_i^{+}-a_i}{b_i},$
obtaining ξ.sub.i.sup.+={1.009, 1.301, 2249, 2.039, 1.268} um;

(47) (f2) calculating the under-lubricated oil film thickness critical value ξ.sub.i.sup.+ of each stand is calculated:

(48) it is assumed that when

(49) $\frac{{\gamma }_i}{{\alpha }_i}=A^{-}=0.6,$
the roll gap is just in an under-lubricated status,

(50) $u_i^{-}=\frac{1}{2\left(2A^{-}-1\right)}\left(\sqrt{\frac{\Delta h_i}{R_i^{\prime }}}+\frac{T_{i0}-T_{i1}}{P_i}\right),$
u.sub.i.sup.−={0.1240, 0.0930, 0.0660, 0.0680, 0.0955};

(51) according to the relationship between the friction coefficient and the oil film thickness: u.sub.i=a.sub.i+b.sub.i.Math.e.sup.B.sup.i.sup..Math.ξ.sup.i, the under-lubricated oil film thickness critical value ξ.sub.i.sup.− of each stand is calculated by the calculation formula

(52) ${\xi }_i^{-}=\frac{1}{B_i}\ln \frac{u_i^{-}-a_i}{b_i},$
obtaining ξ.sub.i.sup.−={0.098, 0.233, 0.401, 0.386, 0.220} um;

(53) subsequently, in the step (f3), the vibration determination index reference value ξ.sub.0i is calculated, wherein

(54) ${\xi }_{0i}=\frac{{\xi }_i^{+}+{\xi }_i^{-}}{2},$
obtaining ξ.sub.0i={0.554, 0.767, 1.325, 1.213, 0.744};

(55) subsequently, in the step (g), the emulsion concentration of each stand is set as C.sub.i={4.2, 4.2, 4.2, 4.2, 4.2} %.

(56) Then, in the step (h), the outlet temperature T.sub.i of the strip steel of each stand is calculated according to the sub-steps shown in the FIG. 3.

(57) Subsequently, in the step (h1), the outlet temperature T.sub.1 of the first stand is calculated as follows:

(58) $T_1=T_1^{\mathrm{Inlet}}+\frac{1-\left({\epsilon }_1/4\right)}{1-\left({\epsilon }_1/2\right)}.Math.\frac{K_1\ln \left(\frac{1}{1-{\epsilon }_1}\right)}{\rho \mathrm{SJ}}=110+\frac{1-\left(0.43/4\right)}{1-\left(0.43/2\right)}.Math.\frac{360\ln \left(\frac{1}{1-0.13}\right)}{7.8.Math.0.47.Math.1}={172.76}^{\circ }C.$

(59) Subsequently, in the step (h2), i is set to 1.

(60) Subsequently, in the step (h3), the temperature of the first section of strip steel behind the outlet of the f0 stand is set to T.sub.i, 1, i.e., T.sub.i, 1=T.sub.i=172.76° C.

(61) Subsequently, in the step (h4), j is set to 2.

(62) Subsequently, in the step (h5), the relationship between the temperature of the j.sup.th section and the temperature of the j−1.sup.th section satisfies the following equation:

(63) $T_{i,j}=-\frac{2k_0{w}^{0.264}\exp \left(9.45-0.1918C_i\right)\times 1.163l}{v_{1i}{h}_{1i}\rho Sm}{T}_{i,j-1}^{-0.213}\left(T_{i,j-1}-T_c\right)+T_{i,j-1},$

(64) wherein k.sub.0 is the influence coefficient of the nozzle shape and the spraying angle, and k.sub.0=1.

(65) Subsequently, in the step (h6), whether the inequation j<m is established is determined, if yes, then setting j=j+1 and turning to step (h5); if no, turning to step (h7).

(66) Subsequently, in the step (h7), the temperature of the 30th section (when m=30) is obtained via iterative calculation: T.sub.1.30=103.32° C.

(67) Subsequently, in the step (h8), the inlet temperature T.sub.2.sup.Inlet of the second stand is calculated as follows: T.sub.2.sup.Inlet=T.sub.1,m=103.32° C.

(68) Subsequently, in the step (h9), the outlet temperature T.sub.2 of the second stand is calculated as follows:

(69) 0$T_2=T_2^{\mathrm{Inlet}}+\frac{1-\left({\epsilon }_2/4\right)}{1-\left({\epsilon }_2/2\right)}.Math.\frac{K_2\ln \left(\frac{1}{1-{\epsilon }_2}\right)}{pSJ}=103.32+\frac{1-\left(0.45/4\right)}{1-\left(0.45/2\right)}.Math.\frac{400\ln \left(\frac{1}{1-0.45}\right)}{7800.Math.0.47.Math.1}=178.02^{\circ }C.$

(70) Subsequently, in the step (h10), whether the inequation i<n is established is determined; if yes, setting i=i+1 and turning to the step (h3); if no, turning to step (h11).

(71) Subsequently, in the step (h11), the outlet temperature of each stand is obtained: T.sub.i={17276, 17802, 186.59, 194.35, 206.33}° C.

(72) Subsequently, in the step (i), the dynamic viscosity η.sub.0i of the emulsion in the roll gap of each stand is calculated by equation: η.sub.0i=b.Math.exp(−a.Math.T.sub.i) (in the equation, a and b are dynamic viscosity parameters of the lubricant under the atmospheric pressure, wherein a=0.05, b=2.5), η.sub.0i={5.39, 5.46, 5.59, 5.69, 5.84} is obtained.

(73) Subsequently, in the step (j), the thickness ξ.sub.i of the oil film in the roll gap of each stand is calculated by the following calculation formula:

(74) ${\xi }_i=\frac{h_{0i}+h_{1i}}{2h_{0i}}.Math.k_c.Math.\frac{3\theta {\eta }_{0i}\left(v_{\mathrm{ri}}+v_{0i}\right)}{{\alpha }_i\left[1-e^{-\theta (K_i\frac{T_{0i}}{h_{0i}.Math.B}}\right]}-k_{\mathrm{rg}}.Math.\left(1+K_{\mathrm{rs}}\right).Math.{\mathrm{Ra}}_{\mathrm{ir}0}.Math.e^{-B_{\mathrm{Li}}.Math.L_i,}$

(75) wherein, k.sub.rg represents the coefficient of the strength of the surface longitudinal roughness of the work roll and the strip steel to entrain the lubricant, wherein k.sub.rg=1.183, K.sub.rs represents the impression rate, i.e., the ratio of transmitting surface roughness of the work roll to the strip steel, wherein K.sub.rs=0.576, and S={0.784, 0.963, 2.101, 2.043, 1.326} um is obtained.

(76) Subsequently, in the step (k), the emulsion concentration comprehensive optimization target function is calculated as follows:

(77) $\{\begin{array}{c}F\left(X\right)=\frac{\lambda }{n}\underset{i=1}{\overset{n}{.Math.}}\sqrt{{\left({\xi }_i-{\xi }_{0i}\right)}^2}+\left(1-\lambda \right)\max .Math.{\xi }_i-{\xi }_{0i}.Math.\\ {\xi }_i^{-}<{\xi }_i<{\xi }_i^{+}\end{array};$

(78) wherein X={C.sub.i} is an optimized variable, and λ=0.5 is a distribution coefficient, and F(X)=0.94 is obtained.

(79) Subsequently, in the step (1), if the equation, F(X)=0.94<F.sub.0=1×10.sup.10, is established, then C.sub.i.sup.y=C.sub.i={4.2, 4.2, 4.2, 4.2, 4.2} %, F.sub.0=F(X)=0.94, and step (m) is performed.

(80) Subsequently, in the step (m), whether the emulsion concentration C.sub.i exceeds the range of the feasible region is determined, if yes, the step (n) is performed; if no, the step (g) is performed.

(81) Subsequently, in the step (n), the optimal emulsion concentration set value C.sub.i.sup.y={4.2, 4.2, 4.5, 4.6, 4.3} % is outputted, wherein C.sub.i.sup.y is the value of C.sub.i when the calculated value of F(X) is minimum in the feasible region.

(82) Finally, during the whole rolling process, the control system of the cold continuous rolling mill set adjusts and controls the emulsion concentration of each stand respectively according to the optimal emulsion concentration set value obtained in the step (n).

(83) To sum up, the technical solution of the invention changes the mode in the prior art that the emulsion in each stand adopts constant concentration control, takes the concentration of the emulsion in each stand as a variable to be optimized, and carries out comprehensive optimization control on the emulsion concentration, thus achieving suppressing the vibration of the rolling mill.

(84) The method of the invention can be widely used in the field of controlling emulsion concentration of the cold continuous rolling mill set.