錘片式粉碎機(jī)設(shè)計(jì)【錘片式飼料粉碎機(jī)】【粉碎飼料】
錘片式粉碎機(jī)設(shè)計(jì)【錘片式飼料粉碎機(jī)】【粉碎飼料】,錘片式飼料粉碎機(jī),粉碎飼料,錘片式粉碎機(jī)設(shè)計(jì)【錘片式飼料粉碎機(jī)】【粉碎飼料】,錘片式,粉碎機(jī),設(shè)計(jì),飼料,粉碎
附錄1 譯 文
摘 要:錘片磨損會破壞錘片式粉碎機(jī)轉(zhuǎn)子的平衡,加劇轉(zhuǎn)子振動。該文的研究目的是基于虛擬樣機(jī)技術(shù)探討錘片磨損對轉(zhuǎn)子振動的影響規(guī)律。采用MDT和vN4D建立了SFSP112×30型錘片式粉碎機(jī)轉(zhuǎn)子的虛擬樣機(jī)模型,對不同錘片磨損情況下粉碎機(jī)轉(zhuǎn)子的振動進(jìn)行了仿真。結(jié)果表明:錘片磨損后,轉(zhuǎn)子振動頻率組成變化不大,而振動幅值和強(qiáng)度變化較大,其中低頻段振動強(qiáng)度增強(qiáng),高頻段振動強(qiáng)度降低;導(dǎo)致轉(zhuǎn)子質(zhì)心徑向偏移的錘片磨損使轉(zhuǎn)子振動幅值和強(qiáng)度均變大,而導(dǎo)致質(zhì)心軸向偏移的磨損對轉(zhuǎn)子振動影響不大;同樣由于轉(zhuǎn)子質(zhì)心的徑向偏移,轉(zhuǎn)子受迫振動頻率強(qiáng)度增加較多。因此,為了降低子運(yùn)轉(zhuǎn)時(shí)的振動,最好避免轉(zhuǎn)子質(zhì)心發(fā)生徑向偏移。
關(guān)鍵詞:錘片式粉碎機(jī)；錘片；虛擬樣機(jī)(VP)；磨損；振動
簡 介
能從谷物中的營養(yǎng)提取出來的飼料粉碎機(jī)已經(jīng)發(fā)展很多年了。但是因?yàn)樗荒芴幚硖厥獾脑希窆阮愂称泛偷V石，所以除了丕林島（地名）的少數(shù)人在研究飼料粉碎機(jī)外，很少人去研究他。盡管飼料粉碎機(jī)已經(jīng)可以解決很多問題，比如振動、噪音、堵塞，用他特有的結(jié)構(gòu)來解決問題，而且可以連續(xù)工作并達(dá)到一定的精度。
雖然一些方法，比如比較低的回轉(zhuǎn)速度，寬的轉(zhuǎn)子直徑被采用，好轉(zhuǎn)了他的性能，但是那些問題不能扯得的被解決。最近，分析了飼料粉碎機(jī)在工作狀態(tài)下轉(zhuǎn)子的轉(zhuǎn)速，旋轉(zhuǎn)的速度能被粉碎機(jī)控制在稍低或者稍高的程度。轉(zhuǎn)子的轉(zhuǎn)速在正常工作下都是不變的，除了在長時(shí)間工作摩擦后。由于錘片的排列或者是其他的因素，產(chǎn)生轉(zhuǎn)子的離心力不固定，所以錘片的磨損是不均衡的，因此，我們要學(xué)習(xí)掌握錘片要磨損時(shí)候的特征，為了使粉碎機(jī)振動保持穩(wěn)定。
實(shí)質(zhì)上的原型技術(shù)（VP）是一個(gè)用cad加工程序代替真實(shí)的模型，為了測試這種產(chǎn)品的特性和特征。這就像電腦的硬件和軟件的發(fā)展，網(wǎng)絡(luò)技術(shù)通過vp技術(shù)開展起來。同時(shí)，傳統(tǒng)的模擬技術(shù)對VP的認(rèn)識理解很有基礎(chǔ)。除了高科技種田，VP技術(shù)還適用于日益發(fā)展的農(nóng)業(yè)機(jī)械設(shè)計(jì)。作者努力的將VP技術(shù)應(yīng)用于工程分析技術(shù)。
對于飼料粉碎機(jī)中轉(zhuǎn)子單一的動力模型，被用來發(fā)展轉(zhuǎn)子動力學(xué)，轉(zhuǎn)子有效的運(yùn)動模型被MDT和VN4D當(dāng)做虛擬原型來用。VP技術(shù)模擬不同情況的磨損下，研究轉(zhuǎn)子轉(zhuǎn)動時(shí)的震動和錘片磨損的分析。
1.單一化轉(zhuǎn)子的模型
SFSP112×30的轉(zhuǎn)子的錘片被均勻的排列，它是由定子、滾球軸承、錘片、軸子組成，最大轉(zhuǎn)速為1480r/min。所以它的最大頻率應(yīng)該是1480/60=24.6Hz。
圖一 SFSP112×30的轉(zhuǎn)子圖表
基于集總的單一化原則叁數(shù)方法 被單一化的模型應(yīng)該有同樣的總質(zhì)量，瞬間的轉(zhuǎn)動慣量有最初的質(zhì)心位置決定。粉碎機(jī)的轉(zhuǎn)子被單一化的分別運(yùn)行在六個(gè)圓盤里。在這系統(tǒng)里，每一個(gè)自我排列的定子，會在壓力的作用下自己運(yùn)行到指定的位置，能夠計(jì)算出他們最后的位置。
2.轉(zhuǎn)子的虛擬原型
轉(zhuǎn)子的3D模型需要建立在一個(gè)MDT的三維建模軟件上，VP的技術(shù)原本是用來實(shí)現(xiàn)Vn4D的，其中包括重要的參數(shù)從轉(zhuǎn)子的發(fā)動機(jī)的功率。一些重要參數(shù)列出如下
（1）定子連接上，平鍵連接被強(qiáng)固連接完全代替；
（2）強(qiáng)固連接也被用來連接圓盤；
（3）因?yàn)檩S子被用來限制錘片的位置，所以強(qiáng)固連接被用來限制軸子和錘片的位置；
（4）在錘片和螺釘通過強(qiáng)固連接，來限制彼此的旋轉(zhuǎn)動作，來完成軸的夾緊；
（5）球軸承被軸襯所代替，軸襯確定參數(shù)。
（6）電動機(jī)的限制被增加到左邊的結(jié)束，他的參數(shù)、轉(zhuǎn)力矩輸出功能被設(shè)置在平衡的感電電動機(jī)上
3.VP技術(shù)的模擬分析
為了要加速模擬速度，唯一的沒有外部的那些環(huán)境應(yīng)用的負(fù)荷被模擬，同時(shí)，粉碎機(jī)需要非常短的加速時(shí)間，沒有負(fù)載的環(huán)境是不可能的。粉碎機(jī)需要加速的這段時(shí)間內(nèi)，轉(zhuǎn)子跑到他的位置上。 錘片的排列的結(jié)果，在研磨中起作用的軸通常用不同種型號，錘片通過定子的排列的長短來確定。因此質(zhì)心上的轉(zhuǎn)子偏離最初的位置。根據(jù)概率公差，質(zhì)心的方向也就是軸運(yùn)動的方向，磨損的方向是在情理之中的。此外，和磨損情形對比，錘片的磨損也是模擬的。
根據(jù)模擬的結(jié)果列出表1
磨損的圖被展現(xiàn)在圖4上，第四個(gè)錘片和軸子被標(biāo)在Ⅰ和Ⅳ上，當(dāng)從軸向觀察，每組的錘片，每組都標(biāo)著1到8平行的定子，在圖4A磨損程度每個(gè)錘片是平等的。圖 4B條的磨損程度，每個(gè)錘片的一組是不平等的，而相應(yīng)的錘片組有Ⅰ ，Ⅲ 同樣的磨損程度。至于Fig.4c和Fig.4d的磨損程度的錘片是不相同完全。圖5顯示振動加速度和動力頻譜圖的球軸承收集在這一過程中，該轉(zhuǎn)子轉(zhuǎn)過第一第二輪之后， 14號實(shí)線代表的振動響應(yīng)左軸承和虛線代表是正確的。 圖4示意圖磨損形式。錘片的磨損的主體部分的振動頻率之前和之后沒有變化。 但強(qiáng)度在每一個(gè)頻率是完全不同的圖5振動響應(yīng)每個(gè)軸承從相應(yīng)的頻率，損壞轉(zhuǎn)子。在低頻階段加強(qiáng)和強(qiáng)度削弱了在高頻率的階段。特別是根據(jù)“甚至磨損”形勢的變化很大大于其他情況下。和同樣的結(jié)論可以發(fā)現(xiàn)振動擴(kuò)增管轉(zhuǎn)子。通過對比Fig.5b和Fig.5c ， 可以推斷，徑向偏移嚴(yán)重破壞了平衡的轉(zhuǎn)子。這一結(jié)論也可以通過Fig.5d和 Fig.5e的對比得到。由于徑向偏移量“相鄰不均勻磨損“顯然是大于“不對稱不均勻磨損” 。強(qiáng)度在強(qiáng)迫振動頻率（24.67赫茲）增加多少更根據(jù)“甚至耐磨”和“相鄰不均勻磨損”的情況，雖然有點(diǎn)變化根據(jù)以上兩種情況對比。
4結(jié)論
?（1）磨損形式并不影響能使錘片的振動頻率改變的轉(zhuǎn)子。然而，它確實(shí)帶來了明顯的變化強(qiáng)度的頻率，其中的強(qiáng)度低頻率的階段，同時(shí)加強(qiáng)這一高頻率階段的削弱。
（2）徑向偏移現(xiàn)實(shí)出來是不穩(wěn)定的轉(zhuǎn)子相對于軸向偏移。振幅和強(qiáng)度大大增加時(shí)質(zhì)心偏離徑向。
（3）強(qiáng)度的強(qiáng)迫振動頻率大大提高時(shí)，會出現(xiàn)無論是錘片磨損均勻或鄰近群體錘片磨損不均等方面的磨損情況。它需要較大的徑向力來抵消這兩個(gè)磨損形式，結(jié)果是不穩(wěn)定的轉(zhuǎn)子。
（4）基于以上這些結(jié)論，為了控制飼料粉碎機(jī)的轉(zhuǎn)子的振動，飼料粉碎機(jī)的轉(zhuǎn)子不應(yīng)徑向偏移。因此，轉(zhuǎn)子需要很好的平衡特別是需要在達(dá)到動態(tài)平衡之前進(jìn)入正常的運(yùn)行。
附錄2 英文參考資料
Vibration generated by the abrasion of the hammer slicein feed-grinder based on virtual prototype technology
Abstract: The abrasion of the hammer slice can cause the rotor of the feed-grinder to lose balance and then make the grinder vibrate. A virtual prototype (VP) based on the rotor of SFSP112×30 feed-grinder was set up by using MDT and vN4D for investigating the relationship between the abrasion of the hammer slice and the vibration of the rotor. By simulating the VP with various abrasion forms, it has been found that the abrasion form does not influence the makeup of the vibration frequency but the intensity. That is, the intensity of the low-frequency stage strengthens but that of the high-frequency stage weakens when the hammer slices are worn out. The vibration amplitude and intensity both increase when the abrasion makes the centroid of the rotor offset radially. However, they do not change much when the centroid offsets axially. The intensity of the forced vibration frequency also greatly rises when the center of mass offsets radially.
Therefore, to damp the vibration of the feed-grinder the centroid of the rotor had better not offset radially.
Key words feed-grinder; hammer slice; virtual prototype (VP); abrasion; vibration
Vibration generated by the abrasion of the hammer slice in feed-grinder based on virtual prototype technology[J]. As one of the kernel equipment in feedstuff processing industry, the feed-grinder has been developed for years. But because of its special processing object, like cereal and mineral, there are few theoreti- cal studies on the feed-grinder except some experimen- tal researches. However, while the feed-grinder runs into many problems such as vibration, noise and clog- ging which mainly result from its own structure char- acteristics, running environment and fitting precision.
Although some methods such as lower rotational speed and wider rotor diameter have been adopted to im-prove its performance, those problems cannot be thor- oughly solved. Recently, et al has analyzed the vibration of the feed-grinder by calculat- ing the natural frequency of the rotor. Therefore, the rotation speed can be adjusted to be lower or high- er than the resonance speed to damp the vibration of the pulverator. But the natural frequency of the rotor is not constant, especially after long time grinding. On account of the array of the hammer slices and other factors, the hammer slices usually abrade unevenly, which causes the eccentricity of the rotor and then make the grinder vibrate[9]. Therefore, studying the characteristics when the hammer slices abrade is quite practical for taking better action to damp the vibration of the pulverator.
Virtual prototype (VP) technology is a process ofusing a CAD model, instead of a physical prototype, to test and evaluate the specific characteristics of a product or a manufacturing process[1]. The develop- ment of hardware and software of computer and network technology widely expands the application of VP. Meanwhile, traditional optimization and simula- tion techniques provide essential foundation to realize VP. Except for the hi-tech field, VP technology has also been applied to agricultural machinery design increasingly[10]. The authors attempt to apply VP technology to the engineering analysis of general machinery.
In this paper a simplified dynamic model for the rotor of the feed-grinder was developed based on rotor dynamics and the corresponding virtual prototype of the rotor was generated by using MDT and vN4D. By simulating the VP under different abrasion situations, the vibration characteristics of the rotor when the hammer slices abrade was analyzed.
1 Simplified model of the rotor
The rotor of SFSP112×30 feed-grinder with the symmetrical hammer slice array is shown in Fig.1. It consists of spindle, ball bearings, disk boards, ham-mer slices, pins and sleeves and its full-load rotational speed is 1480 r/min. So its frequency of the forced vibration should be 1480/60=24.67Hz.
Fig.1 Diagram of the rotor of SFSP112×30 feed-grinder
Based on the simplification principle of lumped parameter method[2]that the simplified model should have the same gross mass, moment of inertia and posi- tion of centroid to the original, the rotor of the pulver- ator was simplified into a one-span six-disc rotor system with two springs' support, as shown in Fig.2. The right end of the spindle and the center of each ball bearing and disk board are chosen as the positions of six disks. Fig.2 Simplified model of the rotor
The ball bearing is generally considered that it only provides stiffness because of its small damping[3]. In the system each self-aligning bearing on one side of the spindle is modeled as a spring, the stiffness of which can be calculated in the light of the following equation[4]:
2 Virtual prototype of the rotor
The 3D model of the rotor which only includes parts related to the simulation was built in MDT, a three- dimensional modeling software. The initialization of VP was fulfilled in vN4D, including importing the 3D model from MDT, modifying constraints between the parts and appending motor power[5]. Some important steps are listed below:
1) Instead of flat key joint each disk board is attached to the spindle by rigid joint which locks two bodies together absolutely.
2)Rigid jointis also used to fasten the pin with the disk board.
3) Because sleeves are used to limit the positions of the hammer slices, rigid joint is set as the constraint between the sleeve and the pin.
4) Constraint between the hammer slice and the pin is revolution joint, which is used to limit the motion of two bodies so that one body only rotates about a certain axis with respect to the other body.
5) The ball bearings are replaced by bushing constraint which can simulate the function of ball bearings. Eq. (1) is set as the stiffness function parameter of bushing constraint.
6) A motor constraint is added to the left end .
3 VP simulation and analysis
In order to accelerate the simulation speed, only those circumstances without external applied load were simulated. Meanwhile, since the pulverator needs a very short accelerating time, only the stage when the rotor runs stably is considered in this paper. As a result of the permutation of the hammer slices, the axial distribution of the material in the mill housing is often inhomogeneous and so does the wear extent of each hammer slice along the spindle. There- fore, the centroid of the rotor deviates from its original position. According to the probable deviation direction of the centroid, namely, radial, axial and both directions, four kinds of abrasion forms were specified. Furthermore, to contrast with the vibration under abrasion situations the performance with undamaged hammer slices was also simulated. The results of simulation are listed in Table 1.Table 1 VP simulation results with five abrasion forms of hammer slices
The diagrammatic sketch of the assumed abrasion forms is shown in Fig. 4. The four pin-and-sleeve groups were labeled fromⅠtoⅣclockwise when viewed from the axial direction and the hammer slices in each group are all marked from 1 to 8 parallel to the spindle. In Fig.4a the worn extent of each hammer slice is equal. In Fig. 4b the worn extent of each hammer slice in one group is unequal while the corresponding hammer slices in groupⅠandⅢhave the same worn extent. As for Fig.4c and Fig.4d the worn extent of the hammer slice is not identical entirely.
Figure 5 shows the vibration acceleration and power spectrum diagram (PSD) of the ball bearings collected in the process that the VP of the rotor ran for one second after it had wheeled for 14 s. Real line represents the vibration response of the left bearing and dashed line represents that of the right one. Fig.4 Sketch of abrasion forms.
The component of the vibration frequency changes little before and after the hammer slices are worn out. But the intensity at each frequency is quite different Fig.5 Vibration response of each bearing from the corresponding frequency of undamaged rotor.
At low-frequency stage the intensity strengthens and weakens at high-frequency stage. Especially the intensity under " even abrasion" situation changes much greater than that under other situations. And the same conclusion can be found for the vibration amplitude of the rotor. By contrasting Fig.5b and Fig.5c, it can be inferred that the radial offset of the centroid badly destroyed the balance of the rotor. This conclusion can also be acquired by contrasting Fig.5d and Fig.5e because the radial offset quantity of "adjacent uneven abrasion" is obviously larger than that of "asymmetric uneven abrasion". The intensity at the forced vibration frequency (24.67Hz) increases much more sharply under " even abrasion" and " adjacent uneven abrasion" situations while it changes a little under the other two situations.
4 Conclusions
1) The abrasion form of hammer slice does not influence the makeup of the vibration frequency of the rotor. However it really brings obvious changes to the intensity of the frequency, which exhibits that the intensity of low-frequency stage strengthens while that of high-frequency stage weakens.
2) The radial offset of the centroid can markedly disrupt the balance of the rotor compared with the axial offset. The vibration amplitude and intensity both increase greatly when the center of mass deviates radially.
3) The intensity at the forced vibration frequency is greatly raised when either the hammer slices wear evenly or the adjacent hammer slice groups wear unevenly with respect to other abrasion forms. It owes to the larger radial centroidal offset of these two abrasion forms that results in the imbalance of the rotor.
4) Based on these conclusions above, in order to damp the vibration of the feed-grinder the centroid of the rotor should not present radial offset. So the rotor needs to be well balanced especially in the dynamic balance test before going into operation.
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