Ginsztler, János

Kator, Lajos

English

Periodica Polytechnica (Budapest University of Technology and Economics)

DETERMINATION ACCURACY OF RELEASED HEAT BY CYLINDRICAL TENSILE SPECIMENS AT THE POINT OF CONTRACTION By L. KATOR and J. GINSZTLER Department for Mechanical Technology. Technical University, Budapest (Received August 6, 1970) 1. Introduction In determining the failure of plastic metals, the amount of mechanical (external) work is to be known as a function of strain. Also the part of residual mechanical energy in the metal, transformed into heat is to be known. Accord-ing to the first principal law of thermodynamics. the energy proportions are expressed by the common relationsbip: (1) where: W'M mechanical (external) work Ws residual mechanical energy in the metal WT residual mechanical energy transformed into heat. According to (1), a certain external work can be constant, though the ratio of the part tram[ormed into heat to that retained in the metal may vary between wide limits. The internal energy variation can be calculated if the othcr two energy members are known. Tests have been done to determine the part of external work transformed into heat on the basis of thermoelectric differences. The thermo-couple was prepared from 0.08 mm 0 copper-constantan wires. The wires were welded on to the surface of the tensile specimen, thus the two branches of the ther-mocouple were connected through the specimen material. To eliminate thermal conduction problems, an adiabatic change of state had to be maintained .. Also, the change of state ought to be kept at a constant rate during deformation. These requirements could be met by tcnsion carried out in short steps, and by selecting suitably refined stages. Deformation in small steps proyides for slight caloric effect. Practically, the test defor-mation stages are to be determined so that the caloric effect can be record-ed at a reliable accuracy. High purity copper was used for the measurements. The basic material was twice remelted in a 10- 6 Hgmm vacuum, by electron beam melting. The resulting 60 mm 0 copper bar was cold rolled to 30 mm 0. After rolling, 28 L. KATOR and J. GISSZTLER the surface was treated by cutting and then holded for 3 hours in protective argon atmosphere at 600°C. The heat-treated bars were processed into tensile specimens 7 mm 0, with a 20 mm long cylindric shaft and a threaded clamping head. Deformation of these specimens consisted in applying stepwise tensile stresses and the released heat was measured as outlined above. 2. Checking the accuracy of surface temperature gauging 2.1. Estimating the character of thermal processes During stepwise deformation of cylindrical tensile specimens and at failure, the surface temperature values were measured at the point of contraction, after each tension, as a function of time. 4TKL {CC] I 0.02 ?:' {sec! Fig. 1. Temperature variation at room temperatur(' vs. time. in broken copper Figure 1 (No. 335) is an excellent example for the character of a series of diagrams. The temperature determination after each deformation lasted To = 0.2 sec. The vertical intercepts of the diagram are proportional to the values of L1T", where TF specimen surface temperature at the point of contraction, TJ ambient temperature: 20°C. The cooling of specimen as a thermal process is to be regarded as llnstationary. While the specimen is cooling, its temperature decreases, and thus heat is transferred to the ambient medium. An object of our experiment was to follow the accuracy of temperature measurement by approximate calculations. It was assumed that that part of external work was transformed into heat which was used to heat the deformed cross-section of the specimen to DETER.11ISATIOS ACCCRACY OF RELEASED HEAT 29 an evenly distributed initial temperature at the moment of deformation. Thus the initial condition was: at the moment of T = 0, T = f(r) = constant. A third-grade boundary condition "was assumed, namely that the surface heat flux density was a function of the surface temperature. Accordingly, the heat conducted from inside the specimen to the surface passes from the surface to the atmosphere by heat transfer, in conformity with the Newtonian law of cooling. As our assumed diagrams, similar to that in Fig. 1, are characteristic of the temperature field resulting from the spatial thermal conduction and the surface heat transfer, our calculations ·were based on this general case. In case of no heat source, the well-known common Fourier differential equation of thermal conduction is the followi,ng: aT _ }. [a~ T I 1 aT I 1 a~ T , a~ T ] -- --,---,-----,-- . aT et;! ar~ r ar r~ a!p~ 8x~ The temperature distribution in the contraction cross-section of the tensile specimen as a function of time, could be determined by several methods. The mathematical solution of the problem has been discussed by CARS LA W and JAEGER [1]. For the solution, the method of finite differences elaborated by SCHMIDT [2] for cylinders may be used. The time-dependent temperature field formation in the specimen can be estimated by geometrical plotting. Development of the unstationary temperature field can also be deter-mined in hydraulic model tests, this method is discussed by FORBERT [3]. A fourth method applied for determining the temperature distribution in the studied cross-section, namely, the solutions by GRIGULL [4] was publish-ed as nomograms, (}c = f(Fo, Bi) and (}", = f(Fo, Bi), where and with notations in Fig. 2. .1J. -::- Tmediu~. ~ - ~riginai Tf- Tp /) fiJ = ----''----'---'If - T;,riginuI Directly, the nomograms only result in the solution of a non-stationary heat conduction case for a cylinder of infinite length. At the same time, however, they are also characteristic of temperature field values as a function of temperature, three-dimensional heat conduction and surface heat transfer, found in tests on contraction cross-section, as a function of time. To take into 30 L. K.1TOR and J. GI.YSZTLER consideration the three-dimensional heat conduction in calculation, the tensile test piece had to be regarded as a short cylinder. Thus, calculations will deliver the developing temperature field as a solution of the general case. It is a well-known fact that, as smaller the length of a cylindrical body, as bigger the surface to volume ratio of the body, and higher the rate of heat propagation. According to MIHEEV [5], short cylinders can h~ tested as T ["C} .+.",:::--_.-t--- Tari()inal 1--==J:;;;;=---+--"'=;;;;;::i:=Tmedium Tr i -'----'--1-- - - ... -- - -I---Ir = 20 cC I Fig. 2. Schematic diagram for notating temperature variations in the tensile specimen hodies resulting from the intersection of a cylinder and a perpendicular plate of the thickness equal to the length of the cylinder. In the above case, the relative surface temperature at the cylinder mid-length equals the product of the relative surface temperature {}", of the infinite length cylinder by the relative temperature Dc at the middle of the infinite plate. Similarly, the relative temperature at the cylinder mid-axis equals the product {}c for the infinite cylinder, by Dt • for the infinite plate. + +1 + + 0,02 0,04 0,06 0,08 -1 Fig. 3. Variation of In f} n. time DETER.\Il.V.~TIO-," ACCURACY OF RELEASED HEAT 31 As there are no thermal sources in the tensile specimen, and both the ambient temperature, Tf , and the surface heat transfer factors (0:) are approxi-mately constant in time, three cooling stages can be discerned: 1. the stage of inordinate process, 2. the regular stage, 3. the stage of thermal balance. As indicated in diagrams In{} = f(r), plotted on basis of the individual .1 Tk = f{r) diagrams, for each case of tension, the regular stage developed some 0.04-0.05 sec after tension, where function In{} = f(r) is well described by rectilinear negative direction tangent [5]. In this case {} = T - Tf , where T j 20°C, and in our case T = TF (Fig. 3, No. 335). 2.2. Time-dependent va.riations in temperature field in the contraction cross-section of tensile specimen To determine the variations in the temperature field, the symbols accord-ing to Fig. 2 were introduced and the values Bc and {} w referring to the tensile specimen - as a short cylinder - were determined after each tension. a) Fig. 4. Shape of the tensile specimen up to the limit of uniform true strain (a) and following the beginning of contraction (h) In our calculations a cylinder length of I = 0.02 m was considered up to the limit of uniform true strain 1..0 = 0.31 while beyond this limit, approxi-mating the deformed volume by a cylinder, the length of the cylinders was considered to equal the prevailing contraction diameter. (The actual shape of the tensile specimen is as in Fig. 4.) Then, the functions {}c = f(Fo, Bi) and BC) = f(Fo, Bi) were solved by means of the relative Grigull-diagrams. .32 L. KATOR and J. GISSZTLER The solution requires knowledge of Bi and Fo with Bi xR i'speCimen and Fo = aT R~ where R radius of the actual contraction cross-section. (For No. 335, R = 0.00176 m.) For the tested copper specimen i. = 340 kcal/m, h, cC, 41 = 0.412 m2.jh, while the x value is to be calculated as follows: The specimen heat content is transferred to the atmosphere by free flow heat transfer after each tension. For determining the heat transfer factor, the observation by MIHEEV was involved, namely that the Nu-number can be produced in every ca15e of this type of heat transfer, as a function of the product of the Cr-number by the Pr-number: Nu = C(Cr . Pr)" where the C and n values can be established in relation to the Cr . Pr product [5]. The x value can be established in knowledge of the thermal characteristics {)f the applied medium: T. 1i+TF ~ 20 QC ref. = -2 Gr 3.43.10-3 .9.81.5.8.10-6 (15.1.10- 6)2 For air: Pr = 0.71. With the above data Cr . Pr = 3.5 . 103 = 0.35 . 101 . As 5.102 < Cr . Pr < 2 . 10', thus c = 0.54 and n = 0.25. On basis of the above thus x= Nu = 0.54 (0.35 . 104)1/4 = 4.12 _ iX·I Nu =--i. air Nu' i, air 4.12·0.0257 ---- = ----- =52 J!m~, s, QC, =44,4kcal/m~, h, QC. I 2.10-3 Therefore Bi DETER.VIISATIO,Y ACCURACY OF RELEASED HEAT 44.4·0.00176 ------ = 0.000227 and thus 340 1 Bi 33 4400. The Fo-number for a cylinder of infinite length was calculated assuming a = 0.412 m2Jh constant while d = 2R values were measurcd after each tension, and the results compiled in Table 1. Table 1 ::\0. d(mm) 335 3.53 1.3692 4.667 The T "alues 'were taken uniformly as T = 0.2 sec, though the jTi, "alues pertaining to T = 0.02 sec were applied for determining functions Oc = f(Fo, Bi) and 0", = f(Fo, Bi). With this step, the certainty and reliability was increased, namely calculating with values T = 0.02 sec, the resulting Fo numhers would be so low that the differences of c1T max - c1T" would he cven less. Similarly, certainty and reliability was increased and thus the real error of temperature gauging was increased too, hy using in the calculations the 1 maximum Bi = 100 value still present in Grigull nomograms instead of the 1 resulting real B' values. ~ I The partial results for No. 335 and the final T medium and Tinitial are indi-cated in Tahle 2. Table 2 ::\0. Dc {}(jJ Ri Fa {}c ":.'C cylinder = cylinder plate plate plate 335 0.89 0.86 100 7.1 0.93 {}c {}" T T :\'0. finite finite JT/: initial medium cylinder ~ylinder (original) 335 0.826 0.80 4.667 25.83 N.82 3 Periodica Polytechnica ~L XV/I. 34 L. KATOR and J. GIXSZTLER 2.3. Checking the accuracy of surface temperature gauging For checking the accuracy of temperature gauging, the formation of surface temperature gauging "error" as a function of the true strain was sought for. The true strain values, )., can be calculated after each tension and, by definition, the "error" of temperature gauging is: LlTmax-LlT" .100 0 / ( F' '» h = /0 see Ig. '"' . . JTk Table 3 indicates the calculation results for our example, :\0. 335. Diagram h = !(}.o) in Fig. 5 was plotted from data in Table 3. The value of h is seen to increase with the increase of plastic strain, hence the accuracy Table 3 .:\"0. Toriginal Tmedium Tp .JTk .dTmax LJT=LJTmax-h, h 0 . • 0 , 335 25.83 24.82 24.667 4.667 4.82 0.153 3.28 of surface temperature gauging decreases. Maximum value of It = hmax = 3.68 0/ 0 was observed in case of )'0 = 1.64. Analysing the above results it has to be emphasized, however, that the real "error" and deviation, in the surface temperature and the specimen axis as o o a2 at, at aB W 1,2 1,1, 1,6 1,8 A Fig. 5. Error in temperature gauging vs. true strain DETER.UISATIOS ACC('RACY OF RELEASED HEAT 35 temperature (in the contraction plane) can be but less than the values obtained by us. As, due to the short time of strain application, the exact, analytical solution would have caused too many problems, a fev.- approximations have been made which undoubtedly increased the real "error". The resulting values (Fig. 5) giye a high-accuracy, reassuring answer as to at what certainty the surface temperature values could be relied on for the metal-physical processes in the specimen centreline. Summary One of the methods for testing the resistance to failure of metals is based on the changes in the energy conditions. According to the first main law of thermodynamics, a part of the external work (lFM) producing plastic strain increases the internal energy (W s) of the metal, while the other part is transformed into heat (WT ). The energy retained in the metal is char-acteristic of the response of the metal to failure. The changes in the material struture can be examined. determining this energy-member, more exactly. The internal energy changes from the external work and the part transformed into heat can be determined by the relationship W,H - WT = Ws. The reliahility of this method depends on how accurately the heat re-leased during strain can be ,! • ~ermined. In our experiment we defined the errors inherent with thermoelectric difference . hermometry in tensile tests, on high-purity copper specimens, i.e. at their point of contraction. Accordingly, the part of mechanical work WT transformed into heat at the point of contraction can be determined at an accuracy of 3.5°{, even in the least favourable case. References 1. CARST.AW, H. 5., JAEGEH, J. C.: Conduction of Heat in Solids. Clarendon Press, Oxford. 1959. 2. PLANK, R.: Handbuch der Kaltetechnik, Springer-Verlag. BerJin-Gottingen-Heidel-berg 1959. 3. FOHBEHT, G.: Hydraulisches :Model! zur Bestimmung von instationarer Temperatur-verteilung. Warme, Volume 75, ~o. 2-3, pp. 100-104. August, 1969. 4. GRIGl.:LL, D.: Temperaturausgleich in einfachen Korpern. Springer-Verlag, Berlin-Gottin-gen-Heidelberg 1964. 5. )IIHEEv, M. A.: Osnovi teploperedachi. Gosenergizdat, Moscow, Leningrad 1949. Dr. Lajos KATOR J [mos GIl\'SZTLER 3* } Budapest XL, Bertalan Lajos u. 7, Hungary 

DETERMINATION ACCURACY OF RELEASED HEAT BY CYLINDRICAL TENSILE SPECIMENS AT THE POINT OF CONTRACTION

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DETERMINATION ACCURACY OF RELEASED HEAT BY CYLINDRICAL TENSILE SPECIMENS AT THE POINT OF CONTRACTION

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Periodica Polytechnica (Budapest University of Technology and Economics)